TWI638057B - Free cutting copper alloy and method for manufacturing the same (2) - Google Patents
Free cutting copper alloy and method for manufacturing the same (2) Download PDFInfo
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- C—CHEMISTRY; METALLURGY
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- C22C9/00—Alloys based on copper
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- C22F1/00—Changing the physical structure of non-ferrous metals or alloys by heat treatment or by hot or cold working
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Abstract
本發明提供一種易削性銅合金,其含有75.0~78.5 %的Cu、2.95~3.55%的Si、0.07~0.28%的Sn、0.06~0.14%的P以及0.022~0.25%的Pb,且剩餘部分包括Zn及不可避免的雜質,組成滿足以下關係:76.2f1=Cu+0.8×Si-8.5×Sn+P+0.5×Pb80.3、61.5f2=Cu-4.3×Si-0.7×Sn-P+0.5×Pb63.3,構成相的面積率(%)滿足以下關係:25κ65、0γ1.5、0β0.2、0μ2.0、97.0f3=α+κ、99.4f4=α+κ+γ+μ、0f5=γ+μ2.5、27f6=κ+6×γ1/2+0.5×μ70,並且,γ相的長邊為40μm以下,μ相的長邊為25μm以下,α相內存在κ相。 The invention provides a free-cutting copper alloy, which contains 75.0 to 78.5% Cu, 2.95 to 3.55% Si, 0.07 to 0.28% Sn, 0.06 to 0.14% P, and 0.022 to 0.25% Pb, and the remainder Including Zn and unavoidable impurities, the composition satisfies the following relationship: 76.2 f1 = Cu + 0.8 × Si-8.5 × Sn + P + 0.5 × Pb 80.3, 61.5 f2 = Cu-4.3 × Si-0.7 × Sn-P + 0.5 × Pb 63.3, the area ratio (%) of the constituent phases satisfies the following relationship: 25 kappa 65, 0 γ 1.5, 0 β 0.2, 0 μ 2.0, 97.0 f3 = α + κ, 99.4 f4 = α + κ + γ + μ, 0 f5 = γ + μ 2.5, 27 f6 = κ + 6 × γ1 / 2 + 0.5 × μ 70, and the long side of the γ phase is 40 μm or less, the long side of the μ phase is 25 μm or less, and the k phase is present in the α phase.
Description
本發明係關於一種具備優異之耐蝕性、優異之衝擊特性、高強度、高溫強度並且大幅減少鉛的含量之易削性銅合金及易削性銅合金的製造方法。尤其關於一種使用於水龍頭、閥、接頭等在人和動物每日攝取之飲用水中使用之器具以及在各種惡劣環境中使用之閥、接頭、閥等電氣/汽車/機械/工業用配管之易削性銅合金及易削性銅合金的製造方法。 The invention relates to a method for manufacturing a free-cutting copper alloy and free-cutting copper alloy having excellent corrosion resistance, excellent impact characteristics, high strength, high-temperature strength, and a significant reduction in lead content. In particular, it is related to an appliance used in faucets, valves, joints and the like used in daily drinking water for humans and animals and valves, joints, and valves used in various harsh environments. Manufacturing method of machinable copper alloy and free-milling copper alloy.
本申請基於2016年8月15日於日本申請之日本專利申請2016-159238號主張優先權,其內容援用於此。 This application claims priority based on Japanese Patent Application No. 2016-159238 filed in Japan on August 15, 2016, the contents of which are incorporated herein by reference.
一直以來,包括飲用水的器具類在內,作為使用於閥、接頭、閥等電氣/汽車/機械/工業用配管之銅合金,一般使用含有56~65mass%的Cu及1~4mass%的Pb且剩餘部分設為Zn之Cu-Zn-Pb合金(所謂的易削黃銅)或含有80~88mass%的Cu、2~8mass%的Sn及2~8mass%的Pb且剩餘部分設為Zn之Cu-Sn-Zn-Pb合金(所謂的青銅:砲 銅)。 Conventionally, copper alloys containing 56 ~ 65mass% Cu and 1 ~ 4mass% Pb have been used as copper alloys used in electrical / automotive / mechanical / industrial piping, including drinking water appliances. And the remaining part is made of Cu-Zn-Pb alloy (so-called free-cutting brass) of Zn or containing 80 ~ 88mass% of Cu, 2 ~ 8mass% of Sn, and 2 ~ 8mass% of Pb, and the remaining part is made of Zn Cu-Sn-Zn-Pb alloy (so-called bronze: gun copper).
然而,近年來Pb對人體和環境的影響變得另人擔憂,各國對Pb的限制運動越發活躍。例如,在美國加利福尼亞州自2010年1月起、又在全美自2014年1月起,關於將飲用水器具等中所含之Pb含量設為0.25mass%以下之限制已生效。又,據了解,關於Pb向飲用水類浸出之浸出量,在將來會限制到5massppm左右。在美國以外的國家,其限制運動亦快速發展,從而要求開發出應對Pb含量的限制之銅合金材料。 However, in recent years, the impact of Pb on the human body and the environment has become worrying, and restrictions on Pb in various countries have become more active. For example, in California, the United States since January 2010, and in the United States since January 2014, restrictions on the Pb content in drinking water appliances and the like to be less than 0.25 mass% have come into effect. It is understood that the leaching amount of Pb to drinking water will be limited to about 5 mass ppm in the future. In countries other than the United States, its restriction movement has also developed rapidly, requiring the development of copper alloy materials that respond to the restrictions on Pb content.
又,在其他產業領域、汽車、機械和電氣/電子設備領域中,例如在歐洲的ELV限制、RoHS限制中易削性銅合金的Pb含量例外地達到4mass%,但與飲用水領域相同地,正在積極討論包括消除例外情況在內之有關Pb含量的限制增強。 In addition, in other industrial fields, automotive, mechanical, and electrical / electronic equipment fields, for example, the Pb content of free-cutting copper alloys in the European ELV and RoHS restrictions has reached 4 mass% except for the same as in the drinking water field. Active enhancements to Pb content including elimination of exceptions are being actively discussed.
該種易削性銅合金的Pb限制增強動向中提倡的是具有切削性功能且含有Bi及Se之銅合金、或在Cu和Zn的合金中藉由增加β相來提高切削性且含有高濃度的Zn之銅合金等,來代替Pb。 The Pb-restriction enhancement trend of this free-cutting copper alloy advocates a copper alloy with a machinability function and containing Bi and Se, or a Cu and Zn alloy by increasing the β phase to improve the machinability and contain a high concentration Instead of Pb.
例如,專利文獻1中提出,如果僅含有Bi來代替Pb則耐蝕性不充分,為了減少β相而使β相孤立,將熱擠壓後的熱擠壓棒緩冷卻至成為180℃進而實施熱處理。 For example, Patent Document 1 proposes that if only Bi is contained instead of Pb, the corrosion resistance is insufficient. In order to reduce the β phase and isolate the β phase, the hot extruded rod after the hot extrusion is slowly cooled to 180 ° C and then heat treated. .
又,專利文獻2中,藉由向Cu-Zn-Bi合金中添加0.7 ~2.5mass%的Sn來析出Cu-Zn-Sn合金的γ相,從而改善耐蝕性。 In Patent Document 2, 0.7 is added to the Cu-Zn-Bi alloy. ~ 2.5mass% of Sn to precipitate the γ phase of Cu-Zn-Sn alloy, thereby improving the corrosion resistance.
然而,如專利文獻1所示,含有Bi來代替Pb之合金在耐蝕性方面存在問題。而且,Bi具有包括可能與Pb相同地對人體有害、由於是稀有金屬而在資源上存在問題、會使銅合金材料變脆之問題等在內的許多問題。此外,如專利文獻1、2中所提出的那樣,即使藉由熱擠壓後的緩冷卻或熱處理來使β相孤立從而提高了耐蝕性,終究無法實現在惡劣環境下的耐蝕性的改善。 However, as shown in Patent Document 1, an alloy containing Bi instead of Pb has a problem in terms of corrosion resistance. In addition, Bi has many problems including the possibility that it is harmful to the human body in the same way as Pb, a problem in resources due to being a rare metal, and a problem that the copper alloy material becomes brittle. In addition, as proposed in Patent Documents 1 and 2, even if the β phase is isolated by slow cooling or heat treatment after hot extrusion to improve the corrosion resistance, the improvement of the corrosion resistance in a harsh environment cannot be achieved after all.
又,如專利文獻2所示,即使Cu-Zn-Sn合金的γ相析出,與α相相比,該γ相本來就缺乏耐蝕性,從而終究無法實現在惡劣環境下的耐蝕性的改善。又,在Cu-Zn-Sn合金中,含有Sn之γ相的切削性功能差到需要與具有切削性功能之Bi一同進行添加。 Further, as shown in Patent Document 2, even if the γ phase of a Cu-Zn-Sn alloy is precipitated, the γ phase inherently lacks corrosion resistance compared to the α phase, so that improvement in corrosion resistance under severe environments cannot be achieved after all. In addition, in the Cu-Zn-Sn alloy, the machinability of the γ phase containing Sn is so poor that it needs to be added together with Bi having machinability.
另一方面,對於含有高濃度的Zn之銅合金,與Pb相比,β相的切削性功能較差,因此不僅終究無法代替含有Pb之易削性銅合金,而且因包含許多β相而耐蝕性尤其耐脫鋅腐蝕性、耐應力腐蝕破裂性非常差。又,該等銅合金由於在高溫(例如150℃)下的強度低,因此例如在烈日下且靠近發動機室的高溫下使用之汽車組件、在高溫/高壓下使用之配管等中無法應對薄壁化、輕量化。 On the other hand, for copper alloys containing a high concentration of Zn, compared with Pb, the machinability of the β phase is poor, so not only cannot replace the free-cutting copper alloy containing Pb, but also corrosion resistance due to the inclusion of many β phases In particular, resistance to dezincification and stress corrosion cracking are very poor. In addition, since these copper alloys have low strength at high temperatures (for example, 150 ° C), they cannot cope with thin walls, such as automotive components used under hot sun and high temperatures near the engine room, and piping used under high temperature / high pressure. Light and lightweight.
此外,Bi使銅合金變脆,若包含許多β相則延展 性降低,因此含有Bi之銅合金或包含許多β相之銅合金不適合作為汽車、機械、電氣用組件以及包括閥在內之飲用水器具材料。再者,對於Cu-Zn合金中含有Sn且包含γ相之黃銅,亦無法改善應力腐蝕破裂,在高溫下的強度低,衝擊特性差,因此不適合使用於該等用途中。 In addition, Bi embrittles the copper alloy and expands if it contains many β phases. Due to its reduced properties, copper alloys containing Bi or copper alloys containing many β phases are not suitable as materials for automobiles, machinery, electrical components, and drinking water appliances including valves. Furthermore, brass containing Cu and Zn phase in the Cu-Zn alloy cannot improve stress corrosion cracking, has low strength at high temperatures, and has poor impact characteristics, and is therefore not suitable for use in these applications.
另一方面,作為易削性銅合金,例如專利文獻3~9中提出含有Si來代替Pb之Cu-Zn-Si合金。 On the other hand, as a free-cutting copper alloy, for example, Patent Documents 3 to 9 propose a Cu-Zn-Si alloy containing Si instead of Pb.
專利文獻3、4中,係藉由主要具有γ相優異之切削性功能,從而藉由不含有Pb或者含有少量Pb來實現優異之切削性者。藉由含有0.3mass%以上的Sn,增加並促進具有切削性功能之γ相的形成,從而改善切削性。又,專利文獻3、4中,藉由形成許多γ相來提高耐蝕性。 In Patent Documents 3 and 4, those having mainly a machinability function having an excellent γ phase are used to achieve excellent machinability by not containing Pb or containing a small amount of Pb. By containing Sn in an amount of 0.3 mass% or more, the formation of a γ phase having a machinability function is increased and promoted, thereby improving machinability. Further, in Patent Documents 3 and 4, corrosion resistance is improved by forming many γ phases.
又,專利文獻5中,設為藉由含有0.02mass%以下的極少量的Pb,並且主要規定γ相、κ相的總計含有面積,從而得到優異之易削性者。此處,Sn作用於形成和增加γ相,從而改善耐沖蝕腐蝕性。 In Patent Document 5, it is assumed that a very small amount of Pb is contained in an amount of 0.02 mass% or less, and the total content area of the γ phase and the κ phase is mainly determined to obtain excellent machinability. Here, Sn acts to form and increase a γ phase, thereby improving erosion corrosion resistance.
此外,專利文獻6、7中提出Cu-Zn-Si合金的鑄件產品,為了實現鑄件晶粒的微細化,在P存在下含有極微量的Zr,並且重視P/Zr的比率等。 In addition, in Patent Documents 6 and 7, casting products of Cu-Zn-Si alloys are proposed. In order to reduce the size of the casting grains, Zr contains a very small amount of Zr in the presence of P, and pays attention to the P / Zr ratio.
又,專利文獻8中提出在Cu-Zn-Si合金中含有Fe之銅合金。 Further, Patent Document 8 proposes a copper alloy containing Fe in a Cu-Zn-Si alloy.
此外,專利文獻9中提出在Cu-Zn-Si合金中含有Sn、 Fe、Co、Ni、Mn之銅合金。 In addition, Patent Document 9 proposes that Cu-Zn-Si alloy contains Sn, Copper alloys of Fe, Co, Ni, Mn.
此處,如專利文獻10和非專利文獻1中所記載,已知在上述Cu-Zn-Si合金中,即使將組成限制於Cu濃度為60mass%以上,Zn濃度為30mass%以下,Si濃度為10mass%以下,除了基地(matrix)α相以外,亦存在β相、γ相、δ相、ε相、ζ相、η相、κ相、μ相、χ相這10種金屬相,根據情況亦存在包含α’、β’、γ’之13種金屬相。 此外,根據經驗眾所周知的是,若增加添加元素,則金相組織變得更加複雜,可能會出現新的相和金屬間化合物,又,由平衡狀態圖得到之合金與實際生產之合金中,在所存在之金屬相的構成中會產生較大偏差。此外,眾所周知該等相的組成亦依銅合金的Cu、Zn、Si等的濃度和加工熱歷程(thermal history)而發生變化。 Here, as described in Patent Literature 10 and Non-Patent Literature 1, it is known that in the above-mentioned Cu-Zn-Si alloy, even if the composition is limited to a Cu concentration of 60 mass% or more, a Zn concentration of 30 mass% or less, and a Si concentration of Below 10mass%, in addition to the matrix α phase, there are 10 metal phases including β phase, γ phase, δ phase, ε phase, ζ phase, η phase, κ phase, μ phase, and χ phase. There are 13 kinds of metal phases including α ', β', and γ '. In addition, it is well known from experience that if an additional element is added, the metallographic structure becomes more complicated, and new phases and intermetallic compounds may appear. In addition, the alloy obtained from the equilibrium state diagram and the alloy actually produced are There is a large deviation in the composition of the existing metal phase. In addition, it is known that the composition of these phases also changes depending on the concentration of Cu, Zn, Si, etc. of the copper alloy and the thermal history of processing.
但是,γ相雖然具有優異之切削性能,但由於Si濃度高且硬而脆,若包含許多γ相,則會在惡劣環境下的耐蝕性、衝擊特性、高溫強度(高溫潛變)等中產生問題。 因此,對於包含大量γ相之Cu-Zn-Si合金,亦與含有Bi之銅合金或包含許多β相之銅合金相同地在其使用上受到限制。 However, although the γ phase has excellent cutting performance, since the Si concentration is high and it is hard and brittle, if many γ phases are included, it will occur in corrosion resistance, impact characteristics, high temperature strength (high temperature creep), etc. under harsh environments. problem. Therefore, the use of a Cu-Zn-Si alloy containing a large amount of γ phases is also limited in the same way as a copper alloy containing Bi or a copper alloy containing many β phases.
再者,專利文獻3~7中所記載之Cu-Zn-Si合金在基於ISO-6509之脫鋅腐蝕試驗中顯示比較良好的結果。然而,在基於ISO-6509之脫鋅腐蝕試驗中,為了判定在一般 水質中的耐脫鋅腐蝕性的良好與否,使用與實際水質完全不同之氯化銅試劑,僅僅以24小時這一短時間進行了評價。 亦即,使用與實際環境不同之試劑以短時間進行評價,因此未能充分評價惡劣環境下的耐蝕性。 Furthermore, the Cu-Zn-Si alloys described in Patent Documents 3 to 7 show relatively good results in the dezincification corrosion test based on ISO-6509. However, in the dezincification corrosion test based on ISO-6509, Whether the dezincification and corrosion resistance in the water was good or not, the copper chloride reagent, which was completely different from the actual water quality, was evaluated in a short time of only 24 hours. That is, the evaluation was performed in a short time using a reagent different from the actual environment, and therefore the corrosion resistance in a severe environment could not be fully evaluated.
又,專利文獻8中提出在Cu-Zn-Si合金中含有Fe之情況。但是,Fe和Si形成比γ相硬而脆之Fe-Si的金屬間化合物。該金屬間化合物存在如下等問題:在切削加工時縮短切削工具的壽命,在研磨時形成硬點而產生外觀上的不良情況。又,將添加元素之Si作為金屬間化合物而進行消耗,從而導致合金的性能下降。 In addition, Patent Document 8 proposes a case where Fe is contained in a Cu-Zn-Si alloy. However, Fe and Si form Fe-Si intermetallic compounds that are harder and more brittle than the γ phase. This intermetallic compound has problems such as shortening the life of a cutting tool during cutting processing, forming hard spots during polishing, and causing a problem in appearance. In addition, the additive element Si is consumed as an intermetallic compound, and the performance of the alloy is reduced.
此外,專利文獻9中,雖然在Cu-Zn-Si合金中添加了Sn和Fe、Co、Mn,但Fe、Co、Mn均與Si進行化合而生成硬而脆之金屬間化合物。因此,與專利文獻8相同地在切削和研磨時產生問題。此外,依專利文獻9,藉由含有Sn、Mn而形成β相,但β相引起嚴重的脫鋅腐蝕,從而提高應力腐蝕破裂的感受性。 In addition, in Patent Document 9, although Cu and Zn-Si alloy are added with Sn, Fe, Co, and Mn, Fe, Co, and Mn all combine with Si to form a hard and brittle intermetallic compound. Therefore, as in Patent Document 8, a problem occurs during cutting and grinding. In addition, according to Patent Document 9, a β phase is formed by containing Sn and Mn, but the β phase causes severe dezincification corrosion, thereby improving the susceptibility to stress corrosion cracking.
【專利文獻1】日本特開2008-214760號公報 [Patent Document 1] Japanese Patent Laid-Open No. 2008-214760
【專利文獻2】國際公開第2008/081947號 [Patent Document 2] International Publication No. 2008/081947
【專利文獻3】日本特開2000-119775號公報 [Patent Document 3] Japanese Patent Laid-Open No. 2000-119775
【專利文獻4】日本特開2000-119774號公報 [Patent Document 4] Japanese Patent Laid-Open No. 2000-119774
【專利文獻5】國際公開第2007/034571號 [Patent Document 5] International Publication No. 2007/034571
【專利文獻6】國際公開第2006/016442號 [Patent Document 6] International Publication No. 2006/016442
【專利文獻7】國際公開第2006/016624號 [Patent Document 7] International Publication No. 2006/016624
【專利文獻8】日本特表2016-511792號公報 [Patent Document 8] Japanese Patent Publication No. 2016-511792
【專利文獻9】日本特開2004-263301號公報 [Patent Document 9] Japanese Patent Laid-Open No. 2004-263301
【專利文獻10】美國專利第4,055,445號說明書 [Patent Document 10] US Patent No. 4,055,445
【非專利文獻1】:美馬源次郎、長谷川正治:伸銅技術研究會誌,2(1963),P.62~77 [Non-Patent Document 1]: Mima Genjiro and Hasegawa Masaharu: Prospects for Copper Technology Research, 2 (1963), P.62 ~ 77
本發明係為了解決這樣的現有技術問題而完成者,其課題為提供一種在惡劣環境下的耐蝕性、衝擊特性、高溫強度優異之易削性銅合金及易削性銅合金的製造方法。再者,本說明書中,除非另有說明,耐蝕性係指耐脫鋅腐蝕性、耐應力腐蝕破裂性這兩者。 The present invention has been made in order to solve such a prior art problem, and an object thereof is to provide a free-cutting copper alloy and a method for manufacturing a free-cutting copper alloy which are excellent in corrosion resistance, impact characteristics, and high-temperature strength under severe environments. In addition, in this specification, unless otherwise stated, corrosion resistance refers to both dezincification resistance and stress corrosion cracking resistance.
為了解決該種課題來實現前述目的,本發明的第1態樣之易削性銅合金的特徵為,含有75.0mass%以上且78.5mass%以下的Cu(銅)、2.95mass%以上且3.55mass%以下的Si(矽)、0.07mass%以上且0.28mass%以下的Sn(錫)、0.06mass%以上且0.14mass%以下的P(磷)以及0.022mass%以上且0.25mass%以下的Pb(鉛),且剩餘部分包括Zn(鋅)及不可避免的雜質,當將Cu的含量設為[Cu]mass%、將Si 的含量設為[Si]mass%、將Sn的含量設為[Sn]mass%、將P的含量設為[P]mass%、將Pb的含量設為[Pb]mass%時,具有如下關係:76.2f1=[Cu]+0.8×[Si]-8.5×[Sn]+[P]+0.5×[Pb]80.3、61.5f2=[Cu]-4.3×[Si]-0.7×[Sn]-[P]+0.5×[Pb]63.3,並且,在金相組織的構成相中,當將α相的面積率設為(α)%、將β相的面積率設為(β)%、將γ相的面積率設為(γ)%、將κ相的面積率設為(κ)%、將μ相的面積率設為(μ)%時,具有如下關係:25(κ)65、0(γ)1.5、0(β)0.2、0(μ)2.0、97.0f3=(α)+(κ)、99.4f4=(α)+(κ)+(γ)+(μ)、0f5=(γ)+(μ)2.5、27f6=(κ)+6×(γ)1/2+0.5×(μ)70,並且,γ相的長邊的長度為40μm以下,μ相的長邊的長度為25μm以下,α相內存在κ相。 In order to solve this problem and achieve the aforementioned object, the free-cutting copper alloy according to the first aspect of the present invention is characterized by containing Cu (copper) of 75.0 mass% or more and 78.5 mass% or less, 2.95 mass% or more and 3.55 masses. % Si (silicon), 0.07 mass% to 0.28 mass% Sn (tin), 0.06 mass% to 0.14 mass% P (phosphorus), and 0.022 mass% to 0.25 mass% Pb ( Lead), and the remainder includes Zn (zinc) and unavoidable impurities. When the content of Cu is [Cu] mass%, the content of Si is [Si] mass%, and the content of Sn is [Sn ] mass%, the content of P is [P] mass%, and the content of Pb is [Pb] mass%, which has the following relationship: 76.2 f1 = [Cu] + 0.8 × [Si] -8.5 × [Sn] + [P] + 0.5 × [Pb] 80.3, 61.5 f2 = [Cu] -4.3 × [Si] -0.7 × [Sn]-[P] + 0.5 × [Pb] 63.3 In the constituent phases of the metallurgical structure, the area ratio of the α phase is (α)%, the area ratio of the β phase is (β)%, and the area ratio of the γ phase is (γ) )%, The area ratio of the κ phase is (κ)%, and the area ratio of the μ phase is (μ)%, which has the following relationship: 25 (κ) 65, 0 (γ) 1.5, 0 (β) 0.2, 0 (μ) 2.0, 97.0 f3 = (α) + (κ), 99.4 f4 = (α) + (κ) + (γ) + (μ), 0 f5 = (γ) + (μ) 2.5, 27 f6 = (κ) + 6 × (γ) 1/2 + 0.5 × (μ) The length of the long side of the γ phase is 40 μm or less, the length of the long side of the μ phase is 25 μm or less, and the κ phase exists in the α phase.
本發明的第2態樣之易削性銅合金的特徵為,在本發明的第1態樣的易削性銅合金中,還含有選自0.02mass%以上且0.08mass%以下的Sb(銻)、0.02mass%以上且 0.08mass%以下的As(砷)、0.02mass%以上且0.30mass%以下的Bi(鉍)之1種或2種以上。 The free-cutting copper alloy according to the second aspect of the present invention is characterized in that the free-cutting copper alloy according to the first aspect of the present invention further contains Sb (antimony selected from 0.02 mass% to 0.08 mass%). ), Above 0.02mass% and One or more of As (arsenic) of 0.08 mass% or less and Bi (bismuth) of 0.02 mass% or more and 0.30 mass% or less.
本發明的第3態樣之易削性銅合金的特徵為,含有75.5mass%以上且78.0mass%以下的Cu、3.1mass%以上且3.4mass%以下的Si、0.10mass%以上且0.27mass%以下的Sn、0.06mass%以上且0.13mass%以下的P以及0.024mass%以上且0.24mass%以下的Pb,且剩餘部分包括Zn及不可避免的雜質,當將Cu的含量設為[Cu]mass%、將Si的含量設為[Si]mass%、將Sn的含量設為[Sn]mass%、將P的含量設為[P]mass%、將Pb的含量設為[Pb]mass%時,具有如下關係:76.6f1=[Cu]+0.8×[Si]-8.5×[Sn]+[P]+0.5×[Pb]79.6、61.7f2=[Cu]-4.3×[Si]-0.7×[Sn]-[P]+0.5×[Pb]63.2,並且,在金相組織的構成相中,當將α相的面積率設為(α)%、將β相的面積率設為(β)%、將γ相的面積率設為(γ)%、將κ相的面積率設為(κ)%、將μ相的面積率設為(μ)%時,具有如下關係:30(κ)56、0(γ)0.8、(β)=0、0(μ)1.0、98.0f3=(α)+(κ)、 99.6f4=(α)+(κ)+(γ)+(μ)、0f5=(γ)+(μ)1.5、32f6=(κ)+6×(γ)1/2+0.5×(μ)62,並且,γ相的長邊的長度為30μm以下,μ相的長邊的長度為15μm以下,α相內存在κ相。 The third aspect of the present invention is characterized in that the free-cutting copper alloy contains 75.5 mass% or more and 78.0 mass% or less of Cu, 3.1 mass% or more and 3.4 mass% or less of Si, 0.10 mass% or more and 0.27 mass% or more. The following Sn, P of 0.06 mass% to 0.13 mass%, and Pb of 0.024 mass% to 0.24 mass%, and the remainder includes Zn and unavoidable impurities. When the content of Cu is set to [Cu] mass When the content of Si is [Si] mass%, the content of Sn is [Sn] mass%, the content of P is [P] mass%, and the content of Pb is [Pb] mass% , Has the following relationship: 76.6 f1 = [Cu] + 0.8 × [Si] -8.5 × [Sn] + [P] + 0.5 × [Pb] 79.6, 61.7 f2 = [Cu] -4.3 × [Si] -0.7 × [Sn]-[P] + 0.5 × [Pb] 63.2 In the constituent phases of the metallurgical structure, the area ratio of the α phase is (α)%, the area ratio of the β phase is (β)%, and the area ratio of the γ phase is (γ) )%, The area ratio of the κ phase is (κ)%, and the area ratio of the μ phase is (μ)%, which has the following relationship: 30 (κ) 56,0 (γ) 0.8, (β) = 0, 0 (μ) 1.0, 98.0 f3 = (α) + (κ), 99.6 f4 = (α) + (κ) + (γ) + (μ), 0 f5 = (γ) + (μ) 1.5, 32 f6 = (κ) + 6 × (γ) 1/2 + 0.5 × (μ) 62, and the length of the long side of the γ phase is 30 μm or less, the length of the long side of the μ phase is 15 μm or less, and the κ phase exists in the α phase.
本發明的第4態樣之易削性銅合金的特徵為,在本發明的第3態樣的易削性銅合金中還含有選自超過0.02mass%且0.07mass%以下的Sb、超過0.02mass%且0.07mass%以下的As、0.02mass%以上且0.20mass%以下的Bi之1種或2種以上。 The free-cutting copper alloy according to the fourth aspect of the present invention is characterized in that the free-cutting copper alloy according to the third aspect of the present invention further contains Sb selected from more than 0.02 mass% to 0.07 mass%, and more than 0.02 One or two or more of As for mass% and 0.07mass% or less, and Bi for 0.02mass% or more and 0.20mass% or less.
本發明的第5態樣之易削性銅合金的特徵為,在本發明的第1~4態樣中任一態樣的易削性銅合金中,作為前述不可避免的雜質之Fe(鐵)、Mn(錳)、Co(鈷)及Cr(鉻)的總量小於0.08mass%。 The free-cutting copper alloy of the fifth aspect of the present invention is characterized in that, in the free-cutting copper alloy of any of the first to fourth aspects of the present invention, Fe (iron) ), Mn (manganese), Co (cobalt) and Cr (chromium) are less than 0.08 mass%.
本發明的第6態樣之易削性銅合金的特徵為,在本發明的第1~5態樣中任一態樣的易削性銅合金中,κ相中所含之Sn的量為0.08mass%以上且0.45mass%以下,κ相中所含之P的量為0.07mass%以上且0.24mass%以下。 The free-cutting copper alloy of the sixth aspect of the present invention is characterized in that, in the free-cutting copper alloy of any of the first to fifth aspects of the present invention, the amount of Sn contained in the κ phase is 0.08 mass% or more and 0.45 mass% or less, and the amount of P contained in the κ phase is 0.07 mass% or more and 0.24 mass% or less.
本發明的第7態樣之易削性銅合金的特徵為,在本發明的第1~6態樣中任一態樣的易削性銅合金中,夏比衝擊試驗(Charpy impact test)值超過14J/cm2且小於50J/cm2,抗拉強度為530N/mm2以上,並且在負載有相當於室溫下 的0.2%保證應力(proof stress)之荷載之狀態下,於150℃保持100小時之後的潛變應變為0.4%以下。再者,夏比衝擊試驗值為U形凹口形狀的試片中的值。 The seventh aspect of the present invention is characterized in that the free-cutting copper alloy has a Charpy impact test value in the free-cutting copper alloy in any of the first to sixth aspects of the present invention. Over 14 J / cm 2 and less than 50 J / cm 2 , tensile strength is 530 N / mm 2 or more, and maintained at 150 ° C under a load equivalent to 0.2% proof stress at room temperature The creep strain after 100 hours is 0.4% or less. The Charpy impact test value is a value in a U-shaped notch-shaped test piece.
本發明的第8態樣之易削性銅合金的特徵為,在本發明的第1~7態樣中任一態樣的易削性銅合金中,使用於自來水管用器具、工業用配管構件、與液體接觸之器具、汽車用組件或電氣產品組件中。 The free-cutting copper alloy according to the eighth aspect of the present invention is characterized in that the free-cutting copper alloy according to any of the first to seventh aspects of the present invention is used for water pipe appliances and industrial piping members. , Appliances that come into contact with liquids, automotive components, or electrical product components.
本發明的第9態樣之易削性銅合金的製造方法係本發明的第1~8態樣中任一態樣的易削性銅合金的製造方法,該方法的特徵為,具有:冷加工製程和熱加工製程中的任意一者或兩者;以及,在前述冷加工製程或前述熱加工製程之後實施之退火製程;在前述退火製程中,在510℃以上且575℃以下的溫度保持20分鐘至8小時、或者在575℃至510℃的溫度區域以0.1℃/分鐘以上且2.5℃/分鐘以下的平均冷卻速度進行冷卻,繼而,在470℃至380℃的溫度區域以超過2.5℃/分鐘且小於500℃/分鐘的平均冷卻速度進行冷卻。 A method for manufacturing a free-cutting copper alloy according to a ninth aspect of the present invention is a method for manufacturing a free-cutting copper alloy according to any one of the first to eighth aspects of the present invention. The method is characterized by having cold working Either or both of the manufacturing process and the hot working process; and the annealing process performed after the aforementioned cold working process or the aforementioned hot working process; in the aforementioned annealing process, the temperature is maintained at a temperature of 510 ° C or higher and 575 ° C or lower for 20 minutes To 8 hours, or cooling at an average cooling rate of 0.1 ° C / min to 2.5 ° C / min in a temperature range of 575 ° C to 510 ° C, and then to exceed 2.5 ° C / min in a temperature range of 470 ° C to 380 ° C It is cooled at an average cooling rate of less than 500 ° C / minute.
本發明的第10態樣之易削性銅合金的製造方法係本發明的第1~8態樣中任一態樣的易削性銅合金的製造方法,該方法的特徵為,包括熱加工製程,進行熱加工時的材料溫度為600℃以上且740℃以下, 當作為前述熱加工而進行熱擠壓時,在冷卻過程中,在470℃至380℃的溫度區域以超過2.5℃/分鐘且小於500℃/分鐘的平均冷卻速度進行冷卻, 當作為前述熱加工而進行熱鍛造時,在冷卻過程中,在575℃至510℃的溫度區域以0.1℃/分鐘以上且2.5℃/分鐘以下的平均冷卻速度進行冷卻,在470℃至380℃的溫度區域以超過2.5℃/分鐘且小於500℃/分鐘的平均冷卻速度進行冷卻。 A method for manufacturing a free-cutting copper alloy according to a tenth aspect of the present invention is a method for manufacturing a free-cutting copper alloy according to any one of the first to eighth aspects of the present invention. The method is characterized by including hot working. In the manufacturing process, the material temperature during hot working is 600 ° C to 740 ° C. When hot extrusion is performed as the aforementioned hot working, during the cooling process, cooling is performed at a temperature range of 470 ° C to 380 ° C at an average cooling rate of more than 2.5 ° C / min and less than 500 ° C / min. When hot forging is performed as the aforementioned hot working, during the cooling process, cooling is performed in a temperature range of 575 ° C to 510 ° C at an average cooling rate of 0.1 ° C / min or more and 2.5 ° C / min or less, and at 470 ° C to 380 ° C. The temperature range was cooled at an average cooling rate of more than 2.5 ° C / min and less than 500 ° C / min.
本發明的第11態樣之易削性銅合金的製造方法係本發明的第1~8態樣中任一態樣的易削性銅合金的製造方法,該方法的特徵為,具有:冷加工製程和熱加工製程中的任意一者或兩者;以及,在前述冷加工製程或前述熱加工製程後實施之低溫退火製程;在前述低溫退火製程中,當將材料溫度設為240℃以上且350℃以下的範圍、將加熱時間設為10分鐘以上且300分鐘以下的範圍、將材料溫度設為T℃、將加熱時間設為t分鐘時,設為150(T-220)×(t)1/2 1200的條件。 The method for producing a free-cutting copper alloy according to the eleventh aspect of the present invention is a method for producing a free-cutting copper alloy according to any one of the first to eighth aspects of the present invention. The method is characterized by having cold working Any one or both of the manufacturing process and the hot working process; and the low-temperature annealing process performed after the cold working process or the hot processing process; in the aforementioned low-temperature annealing process, when the material temperature is set to 240 ° C or higher and 350 The range is below ℃, the heating time is set to a range of 10 minutes to 300 minutes, the material temperature is set to T ° C, and the heating time is set to 150 minutes. (T-220) × (t) 1/2 1200 conditions.
依本發明的態樣,規定了極力減少切削性功能優異但耐蝕性、衝擊特性、高溫強度(高溫潛變)差之γ相,且還盡可能減少對切削性有效之μ相之金相組織。還規定了用於得到該金相組織之組成、製造方法。因此,依本發 明的態樣,能夠提供一種在惡劣環境下的耐蝕性、衝擊特性、延展性、耐磨耗性、常溫強度、高溫強度優異之易削性銅合金及易削性銅合金的製造方法。 According to the aspect of the present invention, it is specified that the γ phase that is excellent in machinability but has poor corrosion resistance, impact characteristics, and high temperature strength (high temperature creep) is specified, and the metallurgical structure of the μ phase that is effective for machinability is reduced as much as possible. . The composition and manufacturing method for obtaining the metallographic structure are also specified. Therefore, according to this The bright aspect can provide a free-cutting copper alloy and a method for manufacturing a free-cutting copper alloy having excellent corrosion resistance, impact characteristics, ductility, wear resistance, normal temperature strength, and high-temperature strength under severe environments.
圖1係實施例1中的易削性銅合金(試驗No.T05)的組織的電子顯微照片。 FIG. 1 is an electron micrograph of a microstructure of a free-cutting copper alloy (Test No. T05) in Example 1. FIG.
圖2係實施例1中的易削性銅合金(試驗No.T53)的組織的金屬顯微照片。 FIG. 2 is a metal micrograph of the structure of a free-cutting copper alloy (Test No. T53) in Example 1. FIG.
圖3係實施例1中的易削性銅合金(試驗No.T53)的組織的電子顯微照片。 FIG. 3 is an electron micrograph of a microstructure of a free-cutting copper alloy (Test No. T53) in Example 1. FIG.
圖4中,(a)係實施例2中的試驗No.T601的在惡劣的水環境下使用8年之後的截面的金屬顯微照片,(b)係試驗No.T602的脫鋅腐蝕試驗1之後的截面的金屬顯微照片,(c)係試驗No.T28的脫鋅腐蝕試驗1之後的截面的金屬顯微照片。 In FIG. 4, (a) is a metal micrograph of a cross section of Test No. T601 in Example 2 after 8 years of use in a severe water environment, and (b) is a dezincification corrosion test 1 of Test No. T602 The metal micrograph of the subsequent section, (c) is the metal micrograph of the section after the dezincification corrosion test 1 of Test No. T28.
以下,對本發明的實施形態之易削性銅合金及易削性銅合金的製造方法進行說明。 Hereinafter, the free-cutting copper alloy and the manufacturing method of the free-cutting copper alloy according to the embodiments of the present invention will be described.
本實施形態之易削性銅合金係作為水龍頭、閥、接頭等在人和動物每日攝取之飲用水中使用之器具、閥、接頭、閥、滑動組件等電氣/汽車/機械/工業用配管構件、與液體 接觸之器具、組件而使用者。 The free-cutting copper alloy of this embodiment is an electrical / automotive / mechanical / industrial piping used as a faucet, a valve, a joint, and the like for appliances, valves, joints, valves, and sliding components used in daily drinking water for humans and animals. Components, and liquids Contact with appliances, components and users.
此處,在本說明書中,如[Zn]這樣帶有括弧之元素記號設為表示該元素的含量(mass%)者。 Here, in this specification, a parenthesized element symbol such as [Zn] is set to indicate the content (mass%) of the element.
而且,本實施形態中,利用該含量的表示方法如下規定複數個組成關係式。 Furthermore, in this embodiment, a method of expressing the content is used to define a plurality of composition relational expressions as follows.
組成關係式f1=[Cu]+0.8×[Si]-8.5×[Sn]+[P]+0.5×[Pb] Composition relationship f1 = [Cu] + 0.8 × [Si] -8.5 × [Sn] + [P] + 0.5 × [Pb]
組成關係式f2=[Cu]-4.3×[Si]-0.7×[Sn]-[P]+0.5×[Pb] Composition relation f2 = [Cu] -4.3 × [Si] -0.7 × [Sn]-[P] + 0.5 × [Pb]
此外,本實施形態中,在金相組織的構成相中設為如下者,亦即,用(α)%表示α相的面積率,用(β)%表示β相的面積率,用(γ)%表示γ相的面積率,用(κ)%表示κ相的面積率,用(μ)%表示μ相的面積率。再者,金相組織的構成相係指α相、γ相、κ相等,並且不含有金屬間化合物、析出物、非金屬夾雜物等。又,存在於α相內之κ相包含於α相的面積率中。所有構成相的面積率之和設為100%。 In addition, in the present embodiment, among the constituent phases of the metallurgical structure, the area ratio of the α phase is represented by (α)%, the area ratio of the β phase is represented by (β)%, and (γ) )% Indicates the area ratio of the γ phase, (κ)% indicates the area ratio of the κ phase, and (μ)% indicates the area ratio of the μ phase. In addition, the constituent phases of the metallographic structure mean that the α phase, the γ phase, and the κ are equal, and do not contain intermetallic compounds, precipitates, nonmetallic inclusions, and the like. The κ phase existing in the α phase is included in the area ratio of the α phase. The sum of the area ratios of all constituent phases is set to 100%.
而且,本實施形態中,如下規定複數個組織關係式。 In this embodiment, a plurality of organizational relational expressions are defined as follows.
組織關係式f3=(α)+(κ) Organization relation f3 = (α) + (κ)
組織關係式f4=(α)+(κ)+(γ)+(μ) Organization relation f4 = (α) + (κ) + (γ) + (μ)
組織關係式f5=(γ)+(μ) Organization relation f5 = (γ) + (μ)
組織關係式f6=(κ)+6×(γ)1/2+0.5×(μ) Organization relationship f6 = (κ) + 6 × (γ) 1/2 + 0.5 × (μ)
本發明的第1實施形態之易削性銅合金含有75.0mass%以上且78.5mass%以下的Cu、2.95mass%以上且 3.55mass%以下的Si、0.07mass%以上且0.28mass%以下的Sn、0.06mass%以上且0.14mass%以下的P以及0.022mass%以上且0.25mass%以下的Pb,且剩餘部分包括Zn及不可避免的雜質。組成關係式f1設在76.2f180.3的範圍內,組成關係式f2設在61.5f263.3的範圍內。κ相的面積率設在25(κ)65的範圍內,γ相的面積率設在0(γ)1.5的範圍內,β相的面積率設在0(β)0.2的範圍內,μ相的面積率設在0(μ)2.0的範圍內。組織關係式f3設在f397.0的範圍內,組織關係式f4設在f499.4的範圍內,組織關係式f5設在0f52.5的範圍內,組織關係式f6設在27f670的範圍內。γ相的長邊的長度設為40μm以下,μ相的長邊的長度設為25μm以下,α相內存在κ相。 The free-cutting copper alloy according to the first embodiment of the present invention contains 75.0 mass% to 78.5 mass% Cu, 2.95 mass% to 3.55 mass% Si, 0.07 mass% to 0.28 mass% Sn, P of 0.06 mass% or more and 0.14 mass% or less, and Pb of 0.022 mass% or more and 0.25 mass% or less, and the remainder includes Zn and unavoidable impurities. The composition relation f1 is set at 76.2 f1 In the range of 80.3, the composition relationship f2 is set at 61.5 f2 Within the range of 63.3. The area ratio of the κ phase is set at 25 (κ) In the range of 65, the area ratio of the γ phase is set to 0 (γ) Within the range of 1.5, the area ratio of the β phase is set at 0 (β) In the range of 0.2, the area ratio of the μ phase is set to 0 (μ) In the range of 2.0. The organizational relationship f3 is set at f3 In the range of 97.0, the organizational relationship f4 is set at f4 Within the range of 99.4, the organizational relationship f5 is set at 0 f5 Within the range of 2.5, the organizational relationship f6 is set at 27 f6 In the range of 70. The length of the long side of the γ phase is 40 μm or less, the length of the long side of the μ phase is 25 μm or less, and the k phase is present in the α phase.
本發明的第2實施形態之易削性銅合金含有75.5mass%以上且78.0mass%以下的Cu、3.1mass%以上且3.4mass%以下的Si、0.10mass%以上且0.27mass%以下的Sn、0.06mass%以上且0.13mass%以下的P以及0.024mass%以上且0.24mass%以下的Pb,且剩餘部分包括Zn及不可避免的雜質。組成關係式f1設在76.6f179.6的範圍內,組成關係式f2設在61.7f263.2的範圍內。κ相的面積率設在30(κ)56的範圍內,γ相的面積率設在0(γ)0.8的範圍內,β相的面積率設為0,μ相的面積率設在0(μ)1.0的範圍內。組織關係式f3設在f398.0的範圍內,組 織關係式f4設在f499.6的範圍內,組織關係式f5設在0f51.5的範圍內,組織關係式f6設在32f662的範圍內。γ相的長邊的長度設為30μm以下,μ相的長邊的長度設為15μm以下,α相內存在κ相。 The free-cutting copper alloy according to the second embodiment of the present invention contains 75.5 mass% or more and 78.0 mass% or less of Cu, 3.1 mass% or more and 3.4 mass% or less of Si, 0.10 mass% or more and 0.27 mass% or less of Sn, P of 0.06 mass% or more and 0.13 mass% or less, and Pb of 0.024 mass% or more and 0.24 mass% or less, and the remainder includes Zn and unavoidable impurities. The composition relation f1 is set at 76.6 f1 In the range of 79.6, the composition relationship f2 is set at 61.7 f2 Within 63.2. The area ratio of the κ phase is set at 30 (κ) Within the range of 56, the area ratio of the γ phase is set to 0 (γ) In the range of 0.8, the area ratio of the β phase is set to 0, and the area ratio of the μ phase is set to 0. (μ) Within the range of 1.0. The organizational relationship f3 is set at f3 Within the range of 98.0, the organizational relationship f4 is set at f4 Within the range of 99.6, the organizational relationship f5 is set at 0 f5 Within the range of 1.5, the organizational relationship f6 is set at 32 f6 Within 62. The length of the long side of the γ phase is 30 μm or less, the length of the long side of the μ phase is 15 μm or less, and the k phase is present in the α phase.
又,本發明的第1實施形態之易削性銅合金中,可以還含有選自0.02mass%以上且0.08mass%以下的Sb、0.02mass%以上且0.08mass%以下的As、0.02mass%以上且0.30mass%以下的Bi之1種或2種以上。 The free-cutting copper alloy according to the first embodiment of the present invention may further contain Sb selected from 0.02 mass% to 0.08 mass%, As, 0.02 mass% to 0.08 mass%, As, and 0.02 mass%. One or two or more Bis of 0.30 mass% or less.
又,本發明的第2實施形態之易削性銅合金中,可以還含有選自超過0.02mass%且0.07mass%以下的Sb、超過0.02mass%且0.07mass%以下的As、0.02mass%以上且0.20mass%以下的Bi之1種或2種以上。 In addition, the free-cutting copper alloy according to the second embodiment of the present invention may further contain Sb selected from more than 0.02 mass% to 0.07 mass%, As, and 0.02 mass% to 0.07 mass%. One or two or more Bis of 0.20 mass% or less.
此外,本發明的第1、2實施形態之易削性銅合金中,κ相中所含之Sn的量為0.08mass%以上且0.45mass%以下,且κ相中所含之P的量為0.07mass%以上且0.24mass%以下為較佳。 In the free-cutting copper alloys according to the first and second embodiments of the present invention, the amount of Sn contained in the κ phase is 0.08 mass% or more and 0.45 mass% or less, and the amount of P contained in the κ phase is It is more preferably 0.07 mass% or more and 0.24 mass% or less.
又,本發明的第1、2實施形態之易削性銅合金中,夏比衝擊試驗值超過14J/cm2且小於50J/cm2,抗拉強度為530N/mm2以上,並且在負載有室溫下的0.2%保證應力(相當於0.2%保證應力之荷載)之狀態下將銅合金於150℃保持100小時之後的潛變應變為0.4%以下為較佳。 Further, first and second embodiments of the present invention the free-cutting copper alloy, the Charpy impact test value exceeds 14J / cm 2 and less than 50J / cm 2, a tensile strength of 530N / mm 2 or more, and loaded with It is preferable that the creep strain of the copper alloy after the copper alloy is kept at 150 ° C for 100 hours under the condition of 0.2% guaranteed stress (equivalent to a load of 0.2% guaranteed stress) at room temperature is 0.4% or less.
以下,對如上述那樣規定成分組成、組成關係式f1、 f2、金相組織、組織關係式f3、f4、f5以及機械特性之理由進行說明。 Hereinafter, the component composition and the composition relationship f1 are defined as described above. The reasons for f2, metallurgical structure, f3, f4, and f5 and mechanical characteristics will be explained.
<成分組成> <Ingredient composition>
(Cu) (Cu)
Cu為本實施形態的合金的主要元素,為了克服本發明的課題,需要至少含有超過75.0mass%之量的Cu。Cu含量小於75.0mass%時,雖然依Si、Zn、Sn的含量、製造製程而不同,但γ相所佔之比例超過1.5%,耐脫鋅腐蝕性、耐應力腐蝕破裂性、衝擊特性、延展性、常溫強度及高溫強度(高溫潛變)差。在某些情況下,有時亦會出現β相。 因此,Cu含量的下限為75.0mass%以上,較佳為75.5mass%以上,更佳為75.8mass%以上。 Cu is the main element of the alloy of this embodiment, and in order to overcome the problem of the present invention, it is necessary to contain at least Cu in an amount exceeding 75.0 mass%. When the Cu content is less than 75.0 mass%, although the content varies according to the content of Si, Zn, and Sn, and the manufacturing process, the proportion of the γ phase exceeds 1.5%, resistance to dezincification, stress corrosion cracking resistance, impact characteristics, and extension Poor performance, normal temperature strength and high temperature strength (high temperature creep). In some cases, β-phase sometimes appears. Therefore, the lower limit of the Cu content is 75.0 mass% or more, preferably 75.5 mass% or more, and more preferably 75.8 mass% or more.
另一方面,Cu含量超過78.5%時,由於大量使用昂貴的銅而成本提高。進而不僅對耐蝕性、常溫強度及高溫強度的效果飽和,而且κ相所佔之比例亦可能變得過多。又,容易析出Cu濃度高的μ相,或在某些情況下容易析出ζ相、χ相。其結果,雖然依金相組織的要件而不同,但可能導致切削性、衝擊特性、熱加工性變差。因此,Cu含量的上限為78.5mass%以下,較佳為78.0mass%以下,更佳為77.5mass%以下。 On the other hand, when the Cu content exceeds 78.5%, the cost increases due to the large amount of expensive copper used. Furthermore, not only the effects of corrosion resistance, normal temperature strength and high temperature strength are saturated, but also the proportion of the κ phase may become excessive. In addition, it is easy to precipitate a μ phase having a high Cu concentration, or in some cases, it is easy to precipitate a ζ phase and a χ phase. As a result, although it depends on the requirements of the metallographic structure, it may cause deterioration of machinability, impact characteristics, and hot workability. Therefore, the upper limit of the Cu content is 78.5 mass% or less, preferably 78.0 mass% or less, and even more preferably 77.5 mass% or less.
(Si) (Si)
Si係為了得到本實施形態的合金的許多優異之特性而 所需之元素。Si有助於形成κ相、γ相、μ相等金屬相。Si提高本實施形態的合金的切削性、耐蝕性、耐應力腐蝕破裂性、強度、高溫強度及耐磨耗性。關於切削性,在α相的情況下,即使含有Si亦幾乎不會改善切削性。但是,由於藉由含有Si而形成之γ相、κ相、μ相等比α相更硬的相,即使不含有大量的Pb,亦能夠具有優異之切削性。然而,隨著γ相或μ相等金屬相所佔之比例增加,會產生延展性和衝擊特性下降的問題、惡劣環境下的耐蝕性下降的問題,以及在可以承受長期使用之高溫潛變特性上產生問題。因此,需要將κ相、γ相、μ相、β相規定在適當的範圍內。 In order to obtain many excellent characteristics of the alloy of this embodiment, the Si system is Required elements. Si contributes to the formation of κ phase, γ phase, and μ metal phases. Si improves the machinability, corrosion resistance, stress corrosion cracking resistance, strength, high temperature strength, and wear resistance of the alloy of this embodiment. Regarding the machinability, in the case of the α phase, the machinability is hardly improved even if Si is contained. However, since the γ phase, the κ phase, and the μ phase, which are formed by containing Si, are harder than the α phase, even if they do not contain a large amount of Pb, they can have excellent machinability. However, as the proportion of the γ phase or μ equivalent metal phase increases, the problems of decreased ductility and impact characteristics, the problem of reduced corrosion resistance in harsh environments, and the high temperature creep characteristics that can withstand long-term use cause problems. Therefore, it is necessary to define the κ phase, γ phase, μ phase, and β phase within appropriate ranges.
又,Si具有在熔解、鑄造時大幅抑制Zn的蒸發之效果,進而隨著增加Si含量,能夠減小比重。 In addition, Si has the effect of significantly suppressing the evaporation of Zn during melting and casting. Further, as the Si content is increased, the specific gravity can be reduced.
為了解決該等金相組織的問題並滿足所有各種特性,雖然依Cu、Zn、Sn等的含量而不同,但Si需要含有2.95mass%以上。Si含量的下限較佳為3.05mass%以上,更佳為3.1mass%以上,進一步較佳為3.15mass%以上。表面上,為了減少Si濃度高的γ相和μ相所佔之比例,認為應降低Si含量。但是,深入研究了與其他元素的摻合比例及製造製程之結果,需要如上述那樣規定Si含量的下限。又,雖然依其他元素的含量、組成的關係式和製造製程而不同,但Si含量約以2.95mass%為界,α相內存在細長的針狀κ 相,並且Si含量約以3.1mass%為界,針狀κ相的量增加。 藉由存在於α相內之κ相,不損害延展性而提高抗拉強度、切削性、衝擊特性、耐磨耗性。以下,亦將存在於α相內之κ相稱為κ1相。 In order to solve these problems of metallographic structure and satisfy all the various characteristics, although it depends on the content of Cu, Zn, Sn, etc., Si needs to contain 2.95 mass% or more. The lower limit of the Si content is preferably 3.05 mass% or more, more preferably 3.1 mass% or more, and still more preferably 3.15 mass% or more. On the surface, in order to reduce the proportion of the γ phase and the μ phase with a high Si concentration, it is considered that the Si content should be reduced. However, as a result of in-depth study of the blending ratio with other elements and the manufacturing process, it is necessary to specify the lower limit of the Si content as described above. Also, although it differs depending on the content of other elements, the relationship between the composition and the manufacturing process, the Si content is bounded by about 2.95 mass%, and there are slender needle-like kappa in the α phase. Phase, and the Si content is about 3.1 mass% as the boundary, the amount of needle-like κ phase increases. The kappa phase existing in the α phase improves tensile strength, machinability, impact characteristics, and abrasion resistance without impairing ductility. Hereinafter, the κ phase existing in the α phase is also referred to as a κ1 phase.
另一方面,若Si含量過多,則由於本實施形態中重視延展性和衝擊特性,使得比α相硬的κ相變得過多而成為問題。因此,Si含量的上限為3.55mass%以下,較佳為3.45mass%以下,更佳為3.4mass%以下,進一步較佳為3.35mass%以下。 On the other hand, if the Si content is too large, the ductility and impact characteristics are emphasized in this embodiment, so that the κ phase, which is harder than the α phase, becomes excessive and becomes a problem. Therefore, the upper limit of the Si content is 3.55 mass% or less, preferably 3.45 mass% or less, more preferably 3.4 mass% or less, and still more preferably 3.35 mass% or less.
(Zn) (Zn)
Zn與Cu、Si一同為本實施形態的合金的主要構成元素,係為了提高切削性、耐蝕性、強度、鑄造性所需之元素。再者,Zn雖然作為剩餘部分而存在,但如果執意要記載,Zn含量的上限約為21.7mass%以下,下限約為17.5mass%以上。 Zn, together with Cu and Si, are main constituent elements of the alloy of this embodiment, and are elements required to improve machinability, corrosion resistance, strength, and castability. In addition, although Zn exists as the remainder, if it is noted that the upper limit of the Zn content is about 21.7 mass% or less, and the lower limit is about 17.5 mass% or more.
(Sn) (Sn)
Sn大幅提高尤其在惡劣環境下的耐脫鋅腐蝕性,並提高耐應力腐蝕破裂性、切削性、耐磨耗性。包括複數個金屬相(構成相)之銅合金中,各金屬相的耐蝕性存在優劣,即使最終成為α相和κ相這2相,亦會從耐蝕性差的相開始腐蝕而腐蝕進展。Sn提高耐蝕性最優異之α相的耐蝕性,並且還同時改善耐蝕性第二優異之κ相的耐蝕性。就Sn而 言,與分佈於α相之量相比,分佈於κ相之量約為1.4倍。亦即分佈於κ相之Sn量為分佈於α相之Sn量的約1.4倍。Sn量增加多少,κ相的耐蝕性隨之進一步提高。隨著Sn含量的增加,α相與κ相的耐蝕性的優劣幾乎消失,或者至少減小α相與κ相的耐蝕性之差,從而大幅提高作為合金的耐蝕性。 Sn significantly improves dezincification and corrosion resistance, especially in harsh environments, and improves stress corrosion cracking resistance, machinability, and abrasion resistance. In a copper alloy including a plurality of metal phases (constituting phases), the corrosion resistance of each metal phase has advantages and disadvantages. Even if it eventually becomes two phases, an α phase and a κ phase, corrosion will begin from the phase with poor corrosion resistance and the corrosion will progress. Sn improves the corrosion resistance of the α phase, which is the most excellent corrosion resistance, and also improves the corrosion resistance of the κ phase, which is the second most excellent corrosion resistance. For Sn In other words, compared to the amount distributed in the α phase, the amount distributed in the κ phase is about 1.4 times. That is, the amount of Sn distributed in the κ phase is about 1.4 times the amount of Sn distributed in the α phase. As the amount of Sn increases, the corrosion resistance of the κ phase further increases. With the increase of the Sn content, the advantages and disadvantages of the corrosion resistance of the α phase and the κ phase almost disappear, or at least the difference between the corrosion resistance of the α phase and the κ phase is reduced, thereby greatly improving the corrosion resistance as an alloy.
然而,含有Sn會促進γ相的形成。Sn自身不具有優異之切削性功能,但藉由形成具有優異之切削性能之γ相,結果提高合金的切削性。另一方面,γ相使合金的耐蝕性、延展性、衝擊特性、延展性、高溫強度變差。與α相相比,Sn分佈於γ相中約10倍至約17倍。亦即分佈於γ相之Sn量為分佈於α相之Sn量的約10倍至約17倍。與不含Sn之γ相相比,在耐蝕性略有改善之程度下,含有Sn之γ相有所不足。這樣,儘管κ相、α相的耐蝕性提高,但在Cu-Zn-Si合金中含有Sn會促進γ相的形成。又,Sn大多分佈於γ相。因此,如果不將Cu、Si、P、Pb這些必要元素設為更加適當的摻合比率並且設為包括製造製程之適當的金相組織狀態,則含有Sn將只能略微提高κ相、α相的耐蝕性,反而因γ相的增大而導致合金的耐蝕性、延展性、衝擊特性、高溫特性降低。又,κ相含有Sn會提高κ相的切削性。其效果隨著與P一同含有Sn而進一步增加。 However, the inclusion of Sn promotes the formation of the γ phase. Sn itself does not have an excellent machinability function, but by forming a γ phase having excellent machinability, the machinability of the alloy is improved as a result. On the other hand, the γ phase deteriorates the corrosion resistance, ductility, impact characteristics, ductility, and high-temperature strength of the alloy. Compared to the α phase, Sn is distributed about 10 times to about 17 times in the γ phase. That is, the amount of Sn distributed in the γ phase is about 10 times to about 17 times the amount of Sn distributed in the α phase. Compared with the γ phase not containing Sn, the γ phase containing Sn is insufficient to the extent that the corrosion resistance is slightly improved. In this way, although the corrosion resistance of the κ phase and the α phase is improved, the inclusion of Sn in the Cu-Zn-Si alloy promotes the formation of the γ phase. In addition, Sn is mostly distributed in the γ phase. Therefore, if the necessary elements such as Cu, Si, P, and Pb are not set to a more appropriate blending ratio and an appropriate metallurgical state including the manufacturing process, the inclusion of Sn will only slightly increase the κ phase and α phase. On the contrary, the increase in the γ phase causes the corrosion resistance, ductility, impact characteristics, and high temperature characteristics of the alloy to decrease. The inclusion of Sn in the κ phase improves the machinability of the κ phase. The effect is further increased as Sn is contained together with P.
藉由控制包括後述之關係式、製造製程在內的金相 組織,能夠製成各種特性優異之銅合金。為了發揮該種效果,需要將Sn的含量的下限設為0.07mass%以上,較佳為0.10mass%以上,更佳為0.12mass%以上。 By controlling the metallography including the relationship and the manufacturing process described below Microstructure can be made into a copper alloy with various characteristics. In order to exert this effect, the lower limit of the content of Sn needs to be 0.07 mass% or more, preferably 0.10 mass% or more, and more preferably 0.12 mass% or more.
另一方面,若Sn含量超過0.28mass%,則γ相所佔之比例增加。作為其對策,需要增加Cu濃度並在金相組織中增加κ相,因此有可能無法獲得更加良好的衝擊特性。Sn含量的上限為0.28mass%以下,較佳為0.27mass%以下,更佳為0.25mass%以下。 On the other hand, if the Sn content exceeds 0.28 mass%, the proportion of the γ phase increases. As a countermeasure for this, it is necessary to increase the Cu concentration and increase the κ phase in the metallurgical structure, so that it may not be possible to obtain more favorable impact characteristics. The upper limit of the Sn content is 0.28 mass% or less, preferably 0.27 mass% or less, and more preferably 0.25 mass% or less.
(Pb) (Pb)
含有Pb會提高銅合金的切削性。約0.003mass%的Pb固熔於基地中,超過該量之Pb作為直徑1μm左右的Pb粒子而存在。Pb即使是微量亦對切削性有效,尤其超過0.02mass%時開始發揮顯著的效果。本實施形態的合金中,由於將切削性能優異之γ相抑制為1.5%以下,因此少量的Pb代替γ相。 Containing Pb improves the machinability of copper alloys. About 0.003 mass% of Pb is solid-melted in the base, and Pb exceeding this amount exists as Pb particles having a diameter of about 1 μm. Pb is effective for machinability even in a small amount, and especially when it exceeds 0.02 mass%, it starts to exhibit a remarkable effect. In the alloy of this embodiment, since the γ phase having excellent cutting performance is suppressed to 1.5% or less, a small amount of Pb is used instead of the γ phase.
因此,Pb的含量的下限為0.022mass%以上,較佳為0.024mass%以上,進一步較佳為0.025mass%以上。尤其在與切削性相關之金相組織的關係式f6的值小於32時,Pb的含量係0.024mass%以上為較佳。 Therefore, the lower limit of the content of Pb is 0.022 mass% or more, preferably 0.024 mass% or more, and still more preferably 0.025 mass% or more. In particular, when the value of the relational expression f6 of the metallographic structure related to machinability is less than 32, the content of Pb is preferably 0.024 mass% or more.
另一方面,Pb對人體有害,且影響衝擊特性及高溫強度。因此,Pb含量的上限為0.25mass%以下,較佳為0.24mass%以下,更佳為0.20mass%以下,最佳為0.10mass% 以下。 On the other hand, Pb is harmful to the human body and affects impact characteristics and high temperature strength. Therefore, the upper limit of the Pb content is 0.25 mass% or less, preferably 0.24 mass% or less, more preferably 0.20 mass% or less, and most preferably 0.10 mass%. the following.
(P) (P)
P與Sn相同地大幅提高尤其在惡劣環境下的耐脫鋅腐蝕性、耐應力腐蝕破裂性。 P and Sn greatly improve the resistance to dezincification and stress corrosion cracking, especially in severe environments.
P與Sn相同地,與分佈於α相之量相比,分佈於κ相之量約為2倍。亦即,分佈於κ相之P量為分佈於α相之P量的約2倍。又,P對提高α相的耐蝕性之效果顯著,但單獨添加P時提高κ相的耐蝕性之效果較小。但是,P藉由與Sn共存,能夠提高κ相的耐蝕性。再者,P幾乎不改善γ相的耐蝕性。又,在κ相含有P會略微提高κ相的切削性。藉由一同添加Sn和P,更有效地改善切削性。 P is the same as Sn, and the amount distributed in the κ phase is approximately twice as much as that in the α phase. That is, the amount of P distributed in the κ phase is about twice the amount of P distributed in the α phase. In addition, the effect of P on improving the corrosion resistance of the α phase is significant, but the effect of improving the corrosion resistance on the κ phase is small when P is added alone. However, by coexisting with Sn, P can improve the corrosion resistance of the κ phase. Furthermore, P hardly improves the corrosion resistance of the γ phase. In addition, the inclusion of P in the κ phase slightly improves the machinability of the κ phase. Adding Sn and P together improves the machinability more effectively.
為了發揮該等效果,P含量的下限為0.06mass%以上,較佳為0.065mass%以上,更佳為0.07mass%以上。 In order to exert these effects, the lower limit of the P content is 0.06 mass% or more, preferably 0.065 mass% or more, and more preferably 0.07 mass% or more.
另一方面,即使含有超過0.14mass%的P,不僅耐蝕性的效果飽和,而且容易形成P和Si的化合物,從而衝擊特性及延展性亦會變差,亦對切削性產生不良影響。因此,P含量的上限為0.14mass%以下,較佳為0.13mass%以下,更佳為0.12mass%以下。 On the other hand, even if P is contained in excess of 0.14 mass%, not only the effect of corrosion resistance is saturated, but also compounds of P and Si are easily formed. As a result, impact characteristics and ductility are deteriorated, and machinability is adversely affected. Therefore, the upper limit of the P content is 0.14 mass% or less, preferably 0.13 mass% or less, and more preferably 0.12 mass% or less.
(Sb、As、Bi) (Sb, As, Bi)
Sb、As均與P、Sn相同地進一步提高尤其在惡劣環境下的耐脫鋅腐蝕性、耐應力腐蝕破裂性。 Sb and As are the same as P and Sn, which further improve the resistance to dezincification and stress corrosion cracking, especially in harsh environments.
為了藉由含有Sb來提高耐蝕性,需要含有0.02mass% 以上的Sb,含有超過0.02mass%的量的Sb為較佳。另一方面,即使含有超過0.08mass%的Sb,耐蝕性提高之效果亦會飽和,γ相反而增加,因此Sb的含量為0.08mass%以下,較佳為0.07mass%以下。 In order to improve corrosion resistance by containing Sb, it is necessary to contain 0.02 mass% The above Sb is preferably Sb in an amount exceeding 0.02 mass%. On the other hand, even if Sb is contained in excess of 0.08 mass%, the effect of improving the corrosion resistance is saturated, and γ is increased on the contrary. Therefore, the content of Sb is 0.08 mass% or less, and preferably 0.07 mass% or less.
又,為了藉由含有As來提高耐蝕性,需要含有0.02mass%以上的As,含有超過0.02mass%的量的As為較佳。另一方面,即使含有超過0.08mass%的As,耐蝕性提高之效果亦會飽和,因此As的含量為0.08mass%以下,較佳為0.07mass%以下。 In addition, in order to improve corrosion resistance by containing As, it is necessary to contain As of 0.02 mass% or more, and it is preferable to contain As in an amount exceeding 0.02 mass%. On the other hand, even if As is contained in excess of 0.08 mass%, the effect of improving the corrosion resistance is saturated. Therefore, the content of As is 0.08 mass% or less, and preferably 0.07 mass% or less.
藉由單獨含有Sb來提高α相的耐蝕性。Sb係熔點比Sn高之低熔點金屬,顯示與Sn類似的行跡,與α相相比,大多分佈於γ相、κ相。Sb藉由與Sn一同添加而具有改善κ相的耐蝕性之效果。然而,無論在單獨含有Sb時還是在與Sn和P一同含有Sb時,改善γ相的耐蝕性之效果均較小。含有過量的Sb反而可能會導致γ相增加。 By including Sb alone, the corrosion resistance of the α phase is improved. Sb is a low-melting-point metal with a higher melting point than Sn, showing similar tracks to Sn. Compared with the α phase, it is mostly distributed in the γ phase and the κ phase. Sb has the effect of improving the corrosion resistance of the κ phase by being added together with Sn. However, the effect of improving the corrosion resistance of the γ phase is small when Sb is contained alone or when Sb is contained together with Sn and P. Containing an excessive amount of Sb may cause an increase in the γ phase.
在Sn、P、Sb、As中,As增強α相的耐蝕性。即使κ相被腐蝕,由於α相的耐蝕性得到提高,因此As發揮阻止在連鎖反應中發生之α相的腐蝕之作用。然而,無論在單獨含有As時還是在與Sn、P、Sb一同含有As時,提高κ相、γ相的耐蝕性之效果均較小。 Among Sn, P, Sb, and As, As enhances the corrosion resistance of the α phase. Even if the κ phase is corroded, since the corrosion resistance of the α phase is improved, As plays a role of preventing the corrosion of the α phase that occurs in a chain reaction. However, the effect of improving the corrosion resistance of the κ phase and the γ phase is small when As is contained alone or when As is contained together with Sn, P, and Sb.
再者,當一同含有Sb、As時,即使Sb、As的總計含量超過0.10mass%,耐蝕性提高之效果亦會飽和,從而延 展性、衝擊特性降低。因此,Sb和As的總量設為0.10mass%以下為較佳。再者,Sb與Sn相同地具有改善κ相的耐蝕性之效果。因此,若[Sn]+0.7×[Sb]的量超過0.12mass%,則作為合金的耐蝕性進一步提高。 Furthermore, when Sb and As are contained together, even if the total content of Sb and As exceeds 0.10 mass%, the effect of improving the corrosion resistance will be saturated, which will delay the Reduced ductility and impact characteristics. Therefore, the total amount of Sb and As is preferably 0.10 mass% or less. In addition, Sb has the effect of improving the corrosion resistance of the κ phase as well as Sn. Therefore, if the amount of [Sn] + 0.7 × [Sb] exceeds 0.12 mass%, the corrosion resistance as an alloy is further improved.
Bi進一步提高銅合金的切削性。為此,需要含有0.02mass%以上的Bi,含有0.025mass%以上的Bi為較佳。 另一方面,雖然Bi對人體的有害性尚不確定,但從對衝擊特性、高溫強度的影響考慮,將Bi的含量的上限設為0.30mass%以下,較佳設為0.20mass%以下,更佳設為0.15mass%以下,進一步較佳設為0.10mass%以下。 Bi further improves the machinability of copper alloys. Therefore, it is necessary to contain Bi of 0.02 mass% or more, and it is preferable to contain Bi of 0.025 mass% or more. On the other hand, although the harmfulness of Bi to the human body is still uncertain, considering the impact on the impact characteristics and high-temperature strength, the upper limit of the content of Bi is set to 0.30 mass% or less, preferably 0.20 mass% or less. It is preferably at most 0.15 mass%, and more preferably at most 0.10 mass%.
(不可避免的雜質) (Unavoidable impurities)
作為本實施形態中的不可避免的雜質,例如可舉出Al、Ni、Mg、Se、Te、Fe、Co、Ca、Zr、Cr、Ti、In、W、Mo、B、Ag及稀土類元素等。 Examples of the unavoidable impurities in this embodiment include Al, Ni, Mg, Se, Te, Fe, Co, Ca, Zr, Cr, Ti, In, W, Mo, B, Ag, and rare earth elements Wait.
一直以來,易削性銅合金以回收之銅合金為主原料,而非以電解銅、電解鋅等優質原料為主。在該領域的下一製程(下游製程、加工製程)中,對大部分構件、組件實施切削加工,相對材料100以40~80的比例產生大量廢棄之銅合金。例如可舉出切屑、切邊、毛邊、橫流道(runner)及包含製造上不良之產品等。該等廢棄之銅合金成為主原料。若切削的切屑等的分離不充分,則從其他易削性銅合金混入Pb、Fe、Se、Te、Sn、P、Sb、As、Ca、Al、Zr、 Ni及稀土類元素。又,切削切屑中含有從工具混入之Fe、W、Co、Mo等。由於廢料含有電鍍之產品,因此混入Ni、Cr。純銅系廢料中混入Mg、Fe、Cr、Ti、Co、In、Ni。從資源的再利用方面以及成本問題考慮,在至少不對特性產生不良影響的範圍內,含有該等元素之切屑等廢料在一定限度內被用作原料。根據經驗,Ni大多從廢料等中混入,Ni的量被允許到小於0.06mass%,小於0.05mass%為較佳。 Fe、Mn、Co、Cr等與Si形成金屬間化合物,在某些情況下與P形成金屬間化合物,從而影響切削性。因此,Fe、Mn、Co、Cr各自的量小於0.05mass%為較佳,小於0.04mass%為更佳。Fe、Mn、Co、Cr的含量的總計亦設為小於0.08mass%為較佳。該總量更佳為小於0.07mass%,進一步較佳為小於0.06mass%。作為其他元素之Al、Mg、Se、Te、Ca、Zr、Ti、In、W、Mo、B、Ag及稀土類元素各自的量小於0.02mass%為較佳,小於0.01mass%為進一步較佳。 For a long time, free-cutting copper alloys are mainly based on recycled copper alloys, rather than high-quality materials such as electrolytic copper and electrolytic zinc. In the next process (downstream process, processing process) in this field, most components and components are subjected to cutting processing, and a large amount of discarded copper alloy is produced at a ratio of 40 to 80 relative to the material 100. Examples include chips, cut edges, burrs, runners, and products that include poor manufacturing. These discarded copper alloys became the main raw materials. If the separation of cutting chips and the like is insufficient, Pb, Fe, Se, Te, Sn, P, Sb, As, Ca, Al, Zr, Ni and rare earth elements. The cutting chips include Fe, W, Co, Mo, and the like mixed in from the tool. Because the scrap contains electroplated products, it is mixed with Ni and Cr. Mg, Fe, Cr, Ti, Co, In, and Ni are mixed into pure copper-based scrap. From the perspective of resource reuse and cost considerations, waste materials such as chips containing these elements are used as raw materials to a certain extent within a range that does not adversely affect the characteristics. According to experience, most of Ni is mixed from waste materials, etc. The amount of Ni is allowed to be less than 0.06 mass%, and preferably less than 0.05 mass%. Fe, Mn, Co, Cr, etc. form an intermetallic compound with Si, and in some cases form an intermetallic compound with P, thereby affecting machinability. Therefore, the amounts of Fe, Mn, Co, and Cr are preferably less than 0.05 mass%, and more preferably less than 0.04 mass%. The total content of Fe, Mn, Co, and Cr is also preferably set to less than 0.08 mass%. The total amount is more preferably less than 0.07 mass%, and still more preferably less than 0.06 mass%. As the other elements, the respective amounts of Al, Mg, Se, Te, Ca, Zr, Ti, In, W, Mo, B, Ag, and rare earth elements are preferably less than 0.02 mass%, and less than 0.01 mass% are further preferable. .
再者,稀土類元素的量為Sc、Y、La、Ce、Pr、Nd、Pm、Sm、Eu、Gd、Tb、Dy、Ho、Er、Tm、Tb及Lu中的1種以上的總量。 The amount of rare earth elements is the total amount of one or more of Sc, Y, La, Ce, Pr, Nd, Pm, Sm, Eu, Gd, Tb, Dy, Ho, Er, Tm, Tb, and Lu. .
(組成關係式f1) (Composition relation f1)
組成關係式f1為表示組成與金相組織之間的關係之公式,即使各元素的量在上述規定之範圍內,如果不滿足該組成關係式f1,則無法滿足本實施形態設為目標之各種特 性。組成關係式f1中,Sn被賦予較大係數-8.5。若組成關係式f1小於76.2,則無論如何在製造製程上花費精力,γ相所佔之比例亦增加,又,γ相的長邊變長,耐蝕性、衝擊特性、高溫特性變差。因此,組成關係式f1的下限為76.2以上,較佳為76.4以上,更佳為76.6以上,進一步較佳為76.8以上。隨著組成關係式f1成為更佳的範圍,γ相的面積率減小,即使存在γ相,γ相亦有被分割之傾向,耐蝕性、衝擊特性、延展性、常溫下的強度、高溫特性進一步提高。 若組成關係式f1的值成為76.6以上,則藉由在製造製程上花費精力,於α相內變得更明顯地存在細長的針狀κ相(κ1相),不損害延展性而提高抗拉強度、切削性、衝擊特性。 The composition relationship formula f1 is a formula showing the relationship between the composition and the metallographic structure. Even if the amount of each element is within the above-mentioned range, if the composition relationship formula f1 is not satisfied, the various targets set in this embodiment cannot be satisfied. special Sex. In the composition relational expression f1, Sn is given a large coefficient of -8.5. If the composition relationship f1 is less than 76.2, no matter how much effort is spent on the manufacturing process, the proportion of the γ phase also increases, and the long side of the γ phase becomes longer, and the corrosion resistance, impact characteristics, and high temperature characteristics become worse. Therefore, the lower limit of the composition relational expression f1 is 76.2 or more, preferably 76.4 or more, more preferably 76.6 or more, and still more preferably 76.8 or more. As the composition relationship f1 becomes a better range, the area ratio of the γ phase decreases. Even if the γ phase exists, the γ phase tends to be divided, corrosion resistance, impact characteristics, ductility, strength at normal temperature, and high temperature characteristics. Further improve. If the value of the composition relational expression f1 is 76.6 or more, the slender needle-like κ phase (κ1 phase) becomes more prominent in the α phase by spending effort on the manufacturing process, and the tensile strength is improved without impairing ductility. Strength, machinability, and impact characteristics.
另一方面,組成關係式f1的上限主要影響κ相所佔之比例,若組成關係式f1大於80.3,則在重視延展性和衝擊特性的情況下,κ相所佔之比例變得過多。又,μ相變得容易析出。若κ相和μ相過多,則衝擊特性、延展性、高溫特性、熱加工性及耐蝕性變差。因此,組成關係式f1的上限為80.3以下,較佳為79.6以下,更佳為79.3以下。 On the other hand, the upper limit of the composition relational expression f1 mainly affects the proportion of the κ phase. If the composition relational expression f1 is greater than 80.3, the proportion of the κ phase becomes excessive when the ductility and impact characteristics are valued. In addition, the μ phase becomes easily precipitated. When there are too many κ phases and μ phases, impact characteristics, ductility, high-temperature characteristics, hot workability, and corrosion resistance deteriorate. Therefore, the upper limit of the composition relational expression f1 is 80.3 or less, preferably 79.6 or less, and even more preferably 79.3 or less.
這樣,藉由將組成關係式f1規定在上述範圍內,可得到特性優異之銅合金。再者,關於作為選擇元素之As、Sb、Bi及另外規定之不可避免的雜質,綜合考慮它們的含量,幾乎不影響組成關係式f1,因此在組成關係式f1中並未規定。 In this way, by setting the composition relationship f1 within the above range, a copper alloy having excellent characteristics can be obtained. In addition, regarding As, Sb, Bi and other unavoidable impurities as selected elements, considering their contents comprehensively, they hardly affect the composition relationship formula f1, so they are not specified in the composition relationship formula f1.
(組成關係式f2) (Composition relation f2)
組成關係式f2為表示組成與加工性、各種特性、金相組織之間的關係之公式。若組成關係式f2小於61.5,則金相組織中的γ相所佔之比例增加,包括β相在內容易出現其他金屬相,又容易殘留,從而耐蝕性、衝擊特性、冷加工性、高溫下的潛變特性變差。又,在熱鍛造時晶粒變得粗大,且容易產生破裂。因此,組成關係式f2的下限為61.5以上,較佳為61.7以上,更佳為61.8以上,進一步較佳為62.0以上。 The composition relational expression f2 is a formula showing the relationship between composition and workability, various characteristics, and metallographic structure. If the composition relationship f2 is less than 61.5, the proportion of the γ phase in the metallurgical structure increases, and other metal phases, including the β phase, tend to appear and remain, which results in corrosion resistance, impact characteristics, cold workability, and high temperature. The creep characteristics deteriorate. Moreover, the crystal grains become coarse during hot forging, and cracks easily occur. Therefore, the lower limit of the composition relational expression f2 is 61.5 or more, preferably 61.7 or more, more preferably 61.8 or more, and even more preferably 62.0 or more.
另一方面,若組成關係式f2超過63.3,則熱變形阻力增大,熱變形能力下降,熱擠出材料和熱鍛造品可能會產生表面破裂。雖然亦與熱加工率和擠出比有關,但例如進行約630℃的熱擠壓、熱鍛造(均為剛進行熱加工後的材料溫度)之熱加工很困難。又,容易出現與熱加工方向平行的方向的長度超過300μm,且寬度超過100μm這樣的粗大的α相。若存在粗大的α相,則切削性下降,α相和存在於κ相的邊界之γ相的長邊的長度變長,強度、耐磨耗性亦降低。又,凝固溫度的範圍亦即(液相線溫度-固相線溫度)會超過50℃,鑄造時的縮孔(shrinkage cavities)變得顯著,無法得到無疵鑄件(sound casting)。因此,組成關係式f2的上限為63.3以下,較佳為63.2以下,更佳為63.0以下。 On the other hand, if the composition relational expression f2 exceeds 63.3, the thermal deformation resistance increases and the thermal deformation ability decreases, and surface cracking may occur in hot extruded materials and hot forged products. Although it is also related to the hot working ratio and extrusion ratio, for example, hot working at about 630 ° C. and hot forging (both the temperature of the material immediately after hot working) are difficult. In addition, a coarse α phase having a length exceeding 300 μm and a width exceeding 100 μm in a direction parallel to the hot working direction tends to occur. When the coarse α phase is present, the machinability is reduced, the length of the long side of the α phase and the γ phase existing at the boundary of the κ phase is increased, and the strength and abrasion resistance are also decreased. In addition, the solidification temperature range (liquid phase temperature-solidus temperature) exceeds 50 ° C., shrinkage cavities during casting become remarkable, and sound casting cannot be obtained. Therefore, the upper limit of the composition relational expression f2 is 63.3 or less, preferably 63.2 or less, and more preferably 63.0 or less.
這樣,藉由將組成關係式f2如上述那样規定在狭小的範圍內,能夠以良好的產率製造特性優異之銅合金。再者,關於作為選擇元素之As、Sb、Bi及另外規定之不可避免的雜質,綜合考慮它們的含量,幾乎不影響組成關係式f2,因此組成關係式f2中並未規定。 As described above, by setting the composition relationship f2 within a narrow range as described above, a copper alloy having excellent characteristics can be produced at a good yield. In addition, regarding As, Sb, Bi and other unavoidable impurities as selected elements, considering their contents comprehensively, it hardly affects the composition relationship formula f2, so it is not specified in the composition relationship formula f2.
(與專利文獻的比較) (Compared with patent literature)
此處,將上述專利文獻3~9中所記載之Cu-Zn-Si合金與本實施形態的合金的組成進行比較之結果示於表1。 Here, Table 1 shows the results of comparing the compositions of the Cu-Zn-Si alloys described in Patent Documents 3 to 9 and the alloys of the present embodiment.
本實施形態與專利文獻3中,Pb及作為選擇元素之Sn的含量不同。本實施形態與專利文獻4中,作為選擇元素之Sn的含量不同。本實施形態與專利文獻5中,Pb的含量不同。本實施形態與專利文獻6、7中,在是否含有Zr方面不同。本實施形態與專利文獻8中,在是否含有Fe方面不同。本實施形態與專利文獻9中,在是否含有Pb方面不同,且在是否含有Fe、Ni、Mn方面亦不同。 This embodiment differs from Patent Document 3 in the content of Pb and Sn as a selective element. This embodiment differs from Patent Document 4 in the content of Sn as a selective element. This embodiment differs from Patent Document 5 in the content of Pb. This embodiment differs from Patent Documents 6 and 7 in whether or not Zr is contained. This embodiment differs from Patent Document 8 in whether Fe is contained. This embodiment differs from Patent Document 9 in whether or not Pb is contained, and also in whether Fe, Ni, and Mn are contained.
如上所述,本實施形態的合金與專利文獻3~9中所記載之Cu-Zn-Si合金中,組成範圍不同。 As described above, the alloys of this embodiment have different composition ranges from the Cu-Zn-Si alloys described in Patent Documents 3 to 9.
<金相組織> <Metallographic structure>
Cu-Zn-Si合金存在10種以上的相,會產生複雜的相變,僅由組成範圍、元素的關係式,未必一定可以得到目標特性。最終藉由指定並確定存在於金相組織中之金屬相的種類及其範圍,能夠得到目標特性。 Cu-Zn-Si alloy has more than 10 kinds of phases, and complex phase transitions will occur. The target characteristics may not necessarily be obtained only by the composition range and the relationship between elements. Finally, by specifying and determining the types and ranges of the metal phases present in the metallographic structure, the target characteristics can be obtained.
在由複數個金屬相構成之Cu-Zn-Si合金的情況下,各相的耐蝕性並不相同而存在優劣。腐蝕從耐蝕性最差的相亦即最容易腐蝕的相,或者從耐蝕性差的相和與該相相鄰的相之間的邊界開始進展。在包括Cu、Zn、Si這3種元素之Cu-Zn-Si合金的情況下,例如若將α相、α’相、β(包括β’)相、κ相、γ(包括γ’)相、μ相的耐蝕性進行比較,則耐蝕性的順序從優異相起依次為α相>α’相>κ相>μ相γ相>β相。κ相與μ相之間的耐蝕性之差尤其大。 In the case of a Cu-Zn-Si alloy composed of a plurality of metal phases, the corrosion resistance of each phase is not the same and there are advantages and disadvantages. Corrosion progresses from the phase with the lowest corrosion resistance, that is, the phase that is most susceptible to corrosion, or from the boundary between the phase with poor corrosion resistance and the phase adjacent to the phase. In the case of a Cu-Zn-Si alloy including three elements of Cu, Zn, and Si, for example, if an α phase, an α 'phase, a β (including β') phase, a κ phase, and a γ (including γ ') phase And μ-phase corrosion resistance, the order of corrosion resistance from superior phase is α phase>α'phase> κ phase> μ phase γ phase> β phase. The difference in corrosion resistance between the κ phase and the μ phase is particularly large.
此處,各相的組成的數值依據合金的組成及各相的佔有面積率而變動,可以說如下。 Here, the numerical value of the composition of each phase varies depending on the composition of the alloy and the occupied area ratio of each phase, and it can be said as follows.
各相的Si濃度從濃度由高到低的順序依次為μ相>γ相>κ相>α相>α’相β相。μ相、γ相及κ相中的Si濃度比合金的Si濃度高。又,μ相的Si濃度為α相的Si濃度的約2.5~約3倍,γ相的Si濃度為α相的Si濃度的約2~約2.5倍。 The order of the Si concentration of each phase from high to low is μ phase> γ phase> κ phase> α phase> α 'phase β-phase. The Si concentration in the μ phase, γ phase, and κ phase is higher than that of the alloy. The Si concentration in the μ phase is about 2.5 to about 3 times the Si concentration in the α phase, and the Si concentration in the γ phase is about 2 to about 2.5 times the Si concentration in the α phase.
各相的Cu濃度從濃度由高到底的順序依次為μ相>κ 相α相>α’相γ相>β相。μ相中的Cu濃度比合金的Cu濃度高。 The Cu concentration of each phase is from μ concentration to κ phase in order from high to low. α phase> α 'phase γ phase> β phase. The Cu concentration in the μ phase is higher than that of the alloy.
專利文獻3~6所示之Cu-Zn-Si合金中,切削性功能最優異之γ相主要與α’相共存,或者存在於與κ相、α相之間的邊界中。γ相在對於銅合金而言惡劣的水質下或環境下,選擇性地成為腐蝕的產生源(腐蝕的起點)而腐蝕進展。當然,如果存在β相,則在γ相腐蝕之前β相開始腐蝕。當μ相與γ相共存時,μ相的腐蝕比γ相略遲或幾乎同時開始。例如當α相、κ相、γ相、μ相共存時,若γ相和μ相選擇性地進行脫鋅腐蝕,則被腐蝕之γ相和μ相藉由脫鋅現象而成為富含Cu之腐蝕生成物,該腐蝕生成物使κ相或鄰近之α’相腐蝕,從而腐蝕連鎖反應性地進展。 In the Cu-Zn-Si alloys shown in Patent Documents 3 to 6, the γ phase having the best machinability function mainly coexists with the α 'phase, or exists in the boundary between the κ phase and the α phase. The γ phase selectively becomes a source of corrosion (origin of corrosion) under the harsh water quality or environment for copper alloys, and the corrosion progresses. Of course, if the β phase is present, the β phase begins to corrode before the γ phase corrodes. When the μ phase and the γ phase coexist, the corrosion of the μ phase starts slightly later or almost simultaneously than the γ phase. For example, when α phase, κ phase, γ phase, and μ phase coexist, if the γ phase and μ phase are selectively dezincified and corroded, the corroded γ phase and μ phase become Cu-rich by dezincification. Corrosion products that corrode the κ phase or the adjacent α 'phase, and the corrosion chain progresses reactively.
再者,包括日本在內世界各地的飲用水的水質多種多樣,並且其水質逐渐成為銅合金容易腐蝕的水質。例如雖然具有上限,但由於對人體的安全性問題而用於消毒目的之殘留氯的濃度增加,作為自來水管用器具之銅合金成為容易腐蝕的環境。如還包含前述汽車組件、機械組件、工業用配管之構件的使用環境那樣,關於夾雜許多溶液之使用環境下的耐蝕性,亦可以說與飲用水相同。 Furthermore, the quality of drinking water around the world, including Japan, is diverse, and its water quality has gradually become the quality of copper alloys that are easily corroded. For example, although it has an upper limit, the concentration of residual chlorine used for sterilization purposes increases due to safety issues to the human body, and the copper alloy as a water pipe appliance becomes a corrosive environment. As with the use environment of the automobile components, mechanical components, and industrial piping components, the corrosion resistance in the use environment containing many solutions can be said to be the same as drinking water.
另一方面,即使控制γ相或γ相、μ相、β相的量, 亦即大幅減少或消除該等各相的存在比例,由α相、α’相、κ相這3相構成之Cu-Zn-Si合金的耐蝕性亦非萬無一失。 依腐蝕環境,耐蝕性比α相差的κ相可能被選擇性地腐蝕,需要提高κ相的耐蝕性。進而,若κ相被腐蝕,則被腐蝕之κ相成為富含Cu之腐蝕生成物而使α相腐蝕,因此亦需要提高α相的耐蝕性。 On the other hand, even if the amount of the γ phase or γ phase, μ phase, and β phase is controlled, That is, the existence ratio of these phases is greatly reduced or eliminated, and the corrosion resistance of the Cu-Zn-Si alloy composed of three phases of α phase, α 'phase, and κ phase is not foolproof. Depending on the corrosive environment, the κ phase, which has a lower corrosion resistance than the α phase, may be selectively corroded, and the corrosion resistance of the κ phase needs to be improved. Furthermore, if the κ phase is corroded, the corroded κ phase becomes a corrosion product rich in Cu and corrodes the α phase. Therefore, it is also necessary to improve the corrosion resistance of the α phase.
又,由於γ相是硬而脆的相,因此在對銅合金構件施加較大負載時,微觀上成為應力集中源。因此,γ相增加應力腐蝕破裂感受性,降低衝擊特性,進而藉由高溫潛變現象來降低高溫強度(高溫潛變強度)。μ相主要存在於α相的晶粒邊界、α相、κ相的相邊界,因此與γ相相同地成為微觀應力集中源。藉由成為應力集中源或晶界滑移現象,μ相增加應力腐蝕破裂感受性,降低衝擊特性,且降低高溫強度。在某些情況下,μ相的存在使該等各種特性變差的程度在γ相以上。 In addition, since the γ phase is a hard and brittle phase, when a large load is applied to a copper alloy member, it becomes a source of stress concentration on a microscopic scale. Therefore, the γ phase increases the susceptibility to stress corrosion cracking, reduces the impact characteristics, and further reduces the high temperature strength (high temperature creep strength) through the high temperature creep phenomenon. The μ phase mainly exists at the grain boundary of the α phase, the phase boundary of the α phase, and the κ phase, and therefore becomes the source of microscopic stress concentration in the same way as the γ phase. By becoming a stress concentration source or grain boundary slip phenomenon, the μ phase increases the sensitivity to stress corrosion cracking, reduces impact characteristics, and reduces high temperature strength. In some cases, the presence of the μ phase deteriorates these various characteristics to a degree greater than the γ phase.
然而,若為了改善耐蝕性和前述各種特性而大幅減少或消除γ相或γ相與μ相的存在比例,則僅藉由含有少量的Pb和α相、α’相、κ相這3相,可能無法得到令人滿意的切削性。因此,為了以含有少量的Pb且具有優異之切削性為前提而改善惡劣的使用環境下的耐蝕性、延展性、衝擊特性、強度及高溫強度,需要如下規定金相組織的構 成相(金屬相、結晶相)。 However, if the γ phase or the ratio of the γ phase to the μ phase is greatly reduced or eliminated in order to improve the corrosion resistance and the aforementioned various characteristics, only by containing a small amount of three phases: Pb and α phase, α ′ phase, and κ phase, Satisfactory machinability may not be obtained. Therefore, in order to improve the corrosion resistance, ductility, impact characteristics, strength, and high-temperature strength under the severe use environment on the premise that it contains a small amount of Pb and has excellent machinability, it is necessary to specify the structure of the metallurgical structure as follows. Phase formation (metal phase, crystalline phase).
再者,以下,各相所佔之比例(存在比例)的單位為面積率(面積%)。 In the following, the unit of the ratio (existence ratio) occupied by each phase is the area ratio (area%).
(γ相) (γ phase)
γ相為最有助於Cu-Zn-Si合金的切削性之相,但為了使惡劣環境下的耐蝕性、強度、高溫特性、衝擊特性成為優異者,不得不限制γ相。為了使耐蝕性成為優異者,需要含有Sn,但含有Sn會進一步增加γ相。為了同時滿足該等矛盾之現象亦即切削性和耐蝕性,限定了Sn、P的含量、組成關係式f1、f2、後述組織關係式及製造製程。 The γ phase is the phase that contributes most to the machinability of the Cu-Zn-Si alloy. However, in order to make the corrosion resistance, strength, high temperature characteristics, and impact characteristics excellent in harsh environments, the γ phase has to be limited. In order to make the corrosion resistance excellent, it is necessary to contain Sn, but the addition of Sn further increases the γ phase. In order to satisfy these contradictory phenomena, that is, machinability and corrosion resistance, the content of Sn and P, the composition relationship formulas f1 and f2, the organization relationship formula described later, and the manufacturing process are limited.
(β相及其他相) (β-phase and other phases)
為了藉由獲得良好的耐蝕性而得到高延展性、衝擊特性、強度、高溫強度,金相組織中所佔之β相、γ相、μ相及ζ相等其他相的比例尤為重要。 In order to obtain high ductility, impact properties, strength, and high-temperature strength by obtaining good corrosion resistance, the ratio of β phase, γ phase, μ phase, and ζ equal to other phases in the metallurgical structure is particularly important.
β相所佔之比例至少需要設為0%以上且0.2%以下,係0.1%以下為較佳,最佳為不存在β相。 The proportion of the β phase needs to be at least 0% to 0.2%, and preferably 0.1% or less, and most preferably, the β phase does not exist.
除α相、κ相、β相、γ相、μ相以外的ζ相等其他相所佔之比例,較佳為0.3%以下,更佳為0.1%以下。最佳為不存在ζ相等其他相。 The proportion of ζ other than the α phase, the κ phase, the β phase, the γ phase, and the μ phase is equal to the proportion of other phases, preferably 0.3% or less, and more preferably 0.1% or less. Most preferably, there are no other phases equal to zeta.
首先,為了得到優異之耐蝕性,需要將γ相所佔之比例設為0%以上且1.5%以下,並且將γ相的長邊的長度 設為40μm以下。 First, in order to obtain excellent corrosion resistance, it is necessary to set the ratio of the γ phase to 0% to 1.5%, and to set the length of the long side of the γ phase. It is set to 40 μm or less.
γ相的長邊的長度藉由以下方法來測定。例如利用500倍或1000倍的金屬顯微照片,在1個視場中測定γ相的長邊的最大長度。如後述,該操作例如在5個視場等複數個任意視場中進行。計算在各視場中得到之γ相的長邊的最大長度的平均值,並作為γ相的長邊的長度。因此,γ相的長邊的長度亦可以說是γ相的長邊的最大長度。 The length of the long side of the γ phase was measured by the following method. For example, the maximum length of the long side of the γ phase is measured in one field of view using a metal micrograph of 500 times or 1000 times. As described later, this operation is performed in a plurality of arbitrary fields of view, such as five fields of view. An average value of the maximum lengths of the long sides of the γ phase obtained in each field of view was calculated and used as the length of the long sides of the γ phase. Therefore, the length of the long side of the γ phase can also be said to be the maximum length of the long side of the γ phase.
γ相所佔之比例係1.0%以下為較佳,設為0.8%以下為進一步較佳,0.5%以下為最佳。雖然依Pb的含量和κ相所佔之比例而不同,但例如當Pb的含量為0.03mass%以下,或κ相所佔之比例為33%以下時,以0.05%以上且小於0.5%的量存在之γ相對耐蝕性等各種特性的影響更小,從而能夠提高切削性。 The ratio of the γ phase is preferably 1.0% or less, more preferably 0.8% or less, and most preferably 0.5% or less. Although it varies depending on the content of Pb and the proportion of κ phase, for example, when the content of Pb is 0.03 mass% or less, or the proportion of κ phase is 33% or less, the amount is 0.05% or more and less than 0.5%. The existence of γ has a smaller influence on various characteristics such as corrosion resistance, and can improve machinability.
由於γ相的長邊的長度影響耐蝕性,因此γ相的長邊的長度為40μm以下,較佳為30μm以下,更佳為20μm以下。 Since the length of the long side of the γ phase affects the corrosion resistance, the length of the long side of the γ phase is 40 μm or less, preferably 30 μm or less, and more preferably 20 μm or less.
γ相的量越多,γ相越容易選擇性地被腐蝕。又,γ相連續得越長,越容易與之相應地選擇性地被腐蝕,腐蝕向深度方向的進展越快。又,被腐蝕之部分越多,越影響存在於被腐蝕之γ相的周圍之α’相和κ相、α相的耐蝕性。 The larger the amount of the γ phase, the easier the γ phase is selectively corroded. Also, the longer the γ phase continues, the easier it is to selectively corrode accordingly, and the faster the corrosion progresses in the depth direction. In addition, the more the corroded portion, the more the corrosion resistance of the α 'phase, the κ phase, and the α phase existing around the corroded γ phase is affected.
γ相所佔之比例及γ相的長邊的長度與Cu、Sn、Si 的含量及組成關係式f1、f2具有很大關連。 The proportion of the γ phase and the length of the long side of the γ phase and Cu, Sn, Si The relationship between the content and composition of f1 and f2 is very relevant.
若γ相變得越多,則延展性、衝擊特性、高溫強度、耐應力腐蝕破裂性變得越差,因此γ相需要為1.5%以下,較佳為1.0%以下,更佳為0.8%以下,最佳為0.5%以下。 存在於金相組織中之γ相在負載有高應力時成為應力集中源。又,結合γ相的結晶結構為BCC的情況,高溫強度降低,且衝擊特性、耐應力腐蝕破裂性降低。其中,當κ相所佔之比例為30%以下時,切削性上多少存在問題,作為對耐蝕性、衝擊特性、延展性、高溫強度影響小的量,亦可以存在0.1%左右的γ相。又,0.1%~1.2%的γ相提高耐磨耗性。 The more the γ phase, the worse the ductility, impact characteristics, high temperature strength, and stress corrosion cracking resistance. Therefore, the γ phase needs to be 1.5% or less, preferably 1.0% or less, and more preferably 0.8% or less. , The best is below 0.5%. The γ phase existing in the metallographic structure becomes a stress concentration source when a high stress is loaded. When the crystal structure of the γ phase is BCC, high-temperature strength is reduced, and impact characteristics and stress corrosion cracking resistance are reduced. Among them, when the proportion of the κ phase is 30% or less, there are some problems in machinability. As a small amount that affects corrosion resistance, impact characteristics, ductility, and high-temperature strength, a γ phase of about 0.1% may exist. In addition, the γ phase of 0.1% to 1.2% improves abrasion resistance.
(μ相) (μphase)
由於μ相雖然具有提高切削性之效果,但從影響耐蝕性以及延展性、衝擊特性、高溫特性方面考慮,至少需要將μ相所佔之比例設為0%以上且2.0%以下。μ相所佔之比例較佳為1.0%以下,更佳為0.3%以下,不存在μ相為最佳。 μ相主要存在於晶粒邊界、相邊界。因此,在惡劣環境下,μ相在μ相所存在之晶粒邊界產生晶界腐蝕。又,若施加衝擊作用,則容易產生以存在於晶界之硬質μ相為起點之裂痕。又,例如在用於汽車的發動機轉動之閥或在高溫高壓氣閥中使用銅合金時,若於150℃的高溫下長時間進行 保持,則晶界容易產生滑移、潛變。因此,需要限制μ相的量,同時將主要存在於晶粒邊界之μ相的長邊的長度設為25μm以下。μ相的長邊的長度較佳為15μm以下,更佳為5μm以下,進一步較佳為4μm以下,最佳為2μm以下。 Although the μ phase has the effect of improving machinability, it is necessary to set the proportion of the μ phase to be at least 0% and 2.0% in terms of affecting corrosion resistance, ductility, impact characteristics, and high temperature characteristics. The proportion of the μ phase is preferably 1.0% or less, more preferably 0.3% or less, and the absence of the μ phase is most preferable. The μ phase mainly exists at grain boundaries and phase boundaries. Therefore, in the harsh environment, grain boundary corrosion occurs at the grain boundary where the μ phase exists. When an impact action is applied, cracks are likely to occur starting from the hard μ phase existing at the grain boundaries. In addition, for example, when a copper alloy is used in a valve for turning an engine of a car or a high-temperature and high-pressure gas valve, it is performed at a high temperature of 150 ° C for a long time. If it is maintained, the grain boundaries are liable to cause slippage and creep. Therefore, it is necessary to limit the amount of the μ phase and to set the length of the long side of the μ phase mainly existing at the grain boundary to 25 μm or less. The length of the long side of the μ phase is preferably 15 μm or less, more preferably 5 μm or less, even more preferably 4 μm or less, and most preferably 2 μm or less.
μ相的長邊的長度可藉由與γ相的長邊的長度的測定方法相同的方法來測定。亦即,依據μ相的大小,例如使用500倍或1000倍的金屬顯微照片或2000倍或5000倍的二次電子像照片(電子顯微照片),在1個視場中測定μ相的長邊的最大長度。該操作在例如5個視場等複數個任意視場中進行。計算在各視場中得到之μ相的長邊的最大長度的平均值,並作為μ相的長邊的長度。因此,μ相的長邊的長度亦可以說是μ相的長邊的最大長度。 The length of the long side of the μ phase can be measured by the same method as the method of measuring the long side of the γ phase. That is, depending on the size of the μ phase, for example, a 500-times or 1000-times metal photomicrograph or a 2000-times or 5000-times secondary electron image photograph (electron micrograph) is used to determine the μ-phase in one field of view. The maximum length of the long side. This operation is performed in a plurality of arbitrary fields of view, such as five fields of view. The average value of the maximum lengths of the long sides of the μ-phase obtained in each field of view was calculated and used as the length of the long sides of the μ-phase. Therefore, the length of the long side of the μ phase can be said to be the maximum length of the long side of the μ phase.
(κ相) (κphase)
在近年來的高速切削條件下,包括切削阻力、切屑排出性在內的材料的切削性能很重要。但是,在將具有最優異之切削性功能之γ相所佔之比例限制在1.5%以下之狀態下,為了具備特別優異之切削性,需要將κ相所佔之比例至少設為25%以上。κ相所佔之比例較佳為30%以上,更佳為32%以上,最佳為34%以上。又,若κ相所佔之比例為滿足切削性之最低限度的量,則富有延展性,衝擊特性優異,耐蝕性、高溫特性、耐磨耗性變得良好。 Under recent high-speed cutting conditions, the cutting performance of materials including cutting resistance and chip discharge is important. However, in a state where the ratio of the γ phase having the most excellent machinability function is limited to 1.5% or less, in order to have particularly excellent machinability, the ratio of the κ phase needs to be at least 25% or more. The proportion of the κ phase is preferably 30% or more, more preferably 32% or more, and most preferably 34% or more. In addition, if the proportion of the κ phase is a minimum amount that satisfies the machinability, the ductility is rich, the impact characteristics are excellent, and the corrosion resistance, high temperature characteristics, and abrasion resistance become good.
硬質的κ相所佔之比例增加並且切削性提高,抗拉強度提高。但是,另一方面,隨著κ相的增加,延展性和衝擊特性逐漸降低。而且,若κ相所佔之比例達到某個恆定量,則切削性提高之效果亦飽和,而且若κ相增加,則切削性反而降低。又,若κ相所佔之比例達到某個恆定量,則隨著延展性的降低,抗拉強度飽和,冷加工性、熱加工性亦變差。當考慮到延展性和衝擊特性的降低、切削性時,需要將κ相所佔之比例設為65%以下。亦即,需要將金相組織中所佔之κ相的比例大致設為2/3以下。κ相所佔之比例較佳為56%以下,更佳為52%以下,最佳為48%以下。 The proportion of the hard κ phase increases, the machinability increases, and the tensile strength increases. However, on the other hand, as the κ phase increases, the ductility and impact characteristics gradually decrease. In addition, if the proportion of the κ phase reaches a certain constant amount, the effect of improving the machinability is also saturated, and if the κ phase increases, the machinability decreases. When the proportion of the κ phase reaches a certain constant amount, as the ductility decreases, the tensile strength becomes saturated, and the cold workability and hot workability also deteriorate. In consideration of reduction in ductility, impact properties, and machinability, the proportion of the κ phase needs to be 65% or less. That is, the ratio of the κ phase in the metallographic structure needs to be approximately 2/3 or less. The proportion of the κ phase is preferably 56% or less, more preferably 52% or less, and most preferably 48% or less.
為了在將切削性能優異之γ相的面積率限制在1.5%以下之狀態下得到優異之切削性,需要提高κ相和α相其自身的切削性。亦即,藉由使κ相中含有Sn、P,κ相的切削性提高。藉由使α相內存在針狀κ相,α相的切削性提高,不過大損害延展性而提高合金的切削性能。作為金相組織中所佔之κ相的比例,為了具備全部延展性、強度、衝擊特性、耐蝕性、高溫特性、切削性及耐磨耗性,最佳為約33%~約52%。 In order to obtain excellent machinability while limiting the area ratio of the γ phase having excellent cutting performance to 1.5% or less, it is necessary to improve the machinability of the κ phase and the α phase. That is, by including Sn, P in the κ phase, the machinability of the κ phase is improved. The presence of the needle-like κ phase in the α phase improves the machinability of the α phase, but greatly reduces the ductility and improves the machinability of the alloy. As the proportion of the κ phase in the metallurgical structure, in order to have all the ductility, strength, impact characteristics, corrosion resistance, high temperature characteristics, machinability, and wear resistance, it is preferably about 33% to 52%.
(α相中的細長的針狀κ相(κ1相)的存在) (Presence of slender needle-like κ phase (κ1 phase) in α phase)
若滿足上述組成、組成關係式、製程的要件,則α相內將存在針狀κ相。該κ相比α相硬。又,α相內的κ相 (κ1相)的厚度為約0.1μm至約0.2μm左右(約0.05μm~約0.5μm),就該κ相(κ1相)而言,厚度薄,細長,且為針狀。藉由使α相中存在厚度薄且細長的針狀κ相(κ1相),能夠得到以下效果。 If the above-mentioned composition, composition relationship, and process requirements are satisfied, a needle-like κ phase will exist in the α phase. This κ is harder than the α phase. The κ phase in the α phase The (κ1 phase) has a thickness of about 0.1 μm to about 0.2 μm (about 0.05 μm to about 0.5 μm). The κ phase (κ1 phase) is thin, slender, and needle-shaped. By having a thin and long acicular κ phase (κ1 phase) in the α phase, the following effects can be obtained.
1)α相增強,作為合金的抗拉強度提高。 1) The α phase is strengthened, and the tensile strength as an alloy is improved.
2)α相的切削性提高,切削阻力和切屑分割性等切削性提高。 2) The machinability of the α phase is improved, and machinability such as cutting resistance and chip splitting ability are improved.
3)由於存在於α相內,因此不對耐蝕性產生不良影響。 3) Since it exists in the α phase, it does not adversely affect the corrosion resistance.
4)α相增強,耐磨耗性提高。 4) The α phase is enhanced, and the abrasion resistance is improved.
存在於α相中之針狀κ相影響Cu、Zn、Si等構成元素和關係式。尤其,若Si量約為2.95%以上,則α相中開始存在針狀κ相(κ1相)。當Si量為約3.05%或約3.1%以上時,更加明顯量的κ1相存在於α相中。當組成關係式f2為63.0以下、進一步為62.5以下時,κ1相變得更容易存在。 The needle-like κ phase existing in the α phase affects the constituent elements and relational expressions such as Cu, Zn, and Si. In particular, if the amount of Si is about 2.95% or more, a needle-like κ phase (κ1 phase) starts to exist in the α phase. When the amount of Si is about 3.05% or more than 3.1%, a more significant amount of the κ1 phase is present in the α phase. When the composition relational expression f2 is 63.0 or less and further 62.5 or less, the κ1 phase becomes more likely to exist.
能夠使用500倍或1000倍左右倍率的金屬顯微鏡來確認析出於α相內且厚度薄之細長的針狀κ相(κ1相)。但是,由於很難計算其面積率,因此α相中的κ1相設為包含於α相的面積率者。 A metal microscope with a magnification of about 500 times or about 1000 times can be used to confirm the slender needle-like kappa phase (κ1 phase) that is precipitated in the α phase and has a thin thickness. However, since it is difficult to calculate the area ratio, the κ1 phase in the α phase is the one included in the α phase.
(組織關係式f3、f4、f5、f6) (Organizational relations f3, f4, f5, f6)
又,為了得到優異之耐蝕性、衝擊特性及高溫強度, 需要α相、κ相所佔之比例的總計(組織關係式f3=(α)+(κ))為97.0%以上。f3的值較佳為98.0%以上,更佳為98.5%以上,最佳為99.0%以上。同樣地,α相、κ相、γ相、μ相所佔之比例的總計(組織關係f4=(α)+(κ)+(γ)+(μ))為99.4%以上,較佳為99.6%以上。 In addition, in order to obtain excellent corrosion resistance, impact characteristics, and high-temperature strength, It is necessary that the total of the proportions of the α phase and the κ phase (organization relationship f3 = (α) + (κ)) is 97.0% or more. The value of f3 is preferably 98.0% or more, more preferably 98.5% or more, and most preferably 99.0% or more. Similarly, the total of the proportions of α phase, κ phase, γ phase, and μ phase (organization relationship f4 = (α) + (κ) + (γ) + (μ)) is 99.4% or more, and preferably 99.6 %the above.
此外,需要γ相、μ相所佔之總計的比例(f5=(γ)+(μ))為2.5%以下。f5的值較佳為1.5%以下,進一步較佳為1.0%以下,最佳為0.5%以下。其中,當κ相的比例低時,切削性略有問題。因此,亦不妨礙以不過度影響衝擊特性的程度含有0.05~0.5%左右的γ相。 In addition, the total ratio (f5 = (γ) + (μ)) of the γ phase and the μ phase is required to be 2.5% or less. The value of f5 is preferably 1.5% or less, more preferably 1.0% or less, and most preferably 0.5% or less. Among them, when the proportion of the κ phase is low, the machinability is slightly problematic. Therefore, it does not prevent the γ phase from being contained in an amount of about 0.05 to 0.5% to such an extent that the impact characteristics are not excessively affected.
此處,在金相組織的關係式f3~f6中,以α相、β相、γ相、δ相、ε相、ζ相、η相、κ相、μ相、χ相這10種金屬相為對象,金屬間化合物、Pb粒子、氧化物、非金屬夾雜物、未熔解物質等不作為對象。又,存在於α相之針狀κ相包含於α相中,在金屬顯微鏡中觀察不到的μ相被排除在外。再者,藉由Si、P及不可避免地混入之元素(例如Fe、Co、Mn)形成之金屬間化合物在金屬相面積率的適用範圍外。但是,該等金屬間化合物影響切削性,因此需要關注不可避免的雜質。 Here, in the relational expressions f3 to f6 of the metallographic structure, there are ten kinds of metal phases: α phase, β phase, γ phase, δ phase, ε phase, ζ phase, η phase, κ phase, μ phase, and χ phase. For the purpose, intermetallic compounds, Pb particles, oxides, non-metallic inclusions, unmelted substances, etc. are not targeted. Needle-like kappa phases existing in the α phase are included in the α phase, and μ phases that are not observed in a metal microscope are excluded. Furthermore, intermetallic compounds formed by Si, P, and unavoidably mixed elements (for example, Fe, Co, Mn) are outside the applicable range of the metal phase area ratio. However, since these intermetallic compounds affect machinability, attention must be paid to unavoidable impurities.
(組織關係式f6) (Organizational relationship f6)
本實施形態的合金中,在Cu-Zn-Si合金中儘管將Pb 的含量保持在最小限度,切削性亦良好,而且尤其需要滿足所有優異之耐蝕性、衝擊特性、延展性、常溫強度、高溫強度。然而,切削性與優異之耐蝕性、衝擊特性係矛盾之特性。 In the alloy of this embodiment, Cu-Zn-Si alloy The content is kept to a minimum, and the machinability is also good. In particular, it is necessary to satisfy all excellent corrosion resistance, impact characteristics, ductility, normal temperature strength, and high temperature strength. However, the machinability is incompatible with the excellent corrosion resistance and impact characteristics.
從金相組織方面考慮,包含越多的切削性能最優異之γ相,切削性越佳,但從耐蝕性、衝擊特性及其他特性方面考慮,不得不減少γ相。得知了當γ相所佔之比例為1.5%以下時,為了得到良好的切削性,需要依實驗結果將上述組織關係式f6的值設在適當的範圍內。 From the perspective of metallographic structure, the more the γ phase with the best cutting performance is included, the better the machinability, but the γ phase has to be reduced in terms of corrosion resistance, impact characteristics and other characteristics. It was found that when the proportion of the γ phase is 1.5% or less, in order to obtain good machinability, it is necessary to set the value of the above-mentioned microstructure relation f6 within an appropriate range according to the experimental results.
γ相的切削性能最優異,但尤其當γ相為少量時,亦即γ相率為1.5%以下時,將比κ相所佔之比例((κ))高6倍之係數提供給γ相所佔之比例((γ)(%))的平方根的值。為了得到良好的切削性能,需要組織關係式f6為27以上。f6的值較佳為32以上,更佳為34以上。當組織關係式f6的值為28~32時,為了得到優異之切削性能,Pb的含量係0.024mass%以上或者κ相中所含之Sn的量係0.11mass%以上為較佳。 The γ phase has the best cutting performance, but especially when the γ phase is small, that is, when the γ phase rate is 1.5% or less, a coefficient that is 6 times higher than the ratio of the κ phase ((κ)) is provided to the γ phase. The value of the square root of the proportion ((γ) (%)). In order to obtain good cutting performance, the structural relationship f6 needs to be 27 or more. The value of f6 is preferably 32 or more, and more preferably 34 or more. When the value of the structural relationship f6 is 28 to 32, in order to obtain excellent cutting performance, it is preferable that the content of Pb is 0.024 mass% or more, or the amount of Sn contained in the κ phase is 0.11 mass% or more.
另一方面,若組織關係式f6超過62或70,則切削性反而變差,並且衝擊特性、延展性明顯變差。因此,需要組織關係式f6為70以下。f6的值較佳為62以下,更佳為56以下。 On the other hand, if the organization relational expression f6 exceeds 62 or 70, the machinability will worsen, and the impact characteristics and ductility will obviously deteriorate. Therefore, the organizational relationship f6 needs to be 70 or less. The value of f6 is preferably 62 or less, and more preferably 56 or less.
(κ相中所含之Sn、P的量) (Amounts of Sn and P contained in the κ phase)
為了提高κ相的耐蝕性,於合金中含有0.07mass%以上且0.28mass%以下的量的Sn,並且含有0.06mass%以上且0.14mass%以下的量的P為較佳。 In order to improve the corrosion resistance of the κ phase, Sn is preferably contained in the alloy in an amount of 0.07 mass% or more and 0.28 mass% or less, and P is contained in an amount of 0.06 mass% or more and 0.14 mass% or less.
本實施形態的合金中,Sn的含量為0.07~0.28mass%時,且將分佈於α相之Sn量設為1時,Sn以於κ相中約1.4、於γ相中約10~約17、於μ相中約2~約3的比例被分佈。藉由在製造製程上花費精力,亦能夠將分佈於γ相之量減少為分佈於α相之量的約10倍。例如,在本實施形態的合金的情況下,在含有0.2mass%的量的Sn之Cu-Zn-Si-Sn合金中α相所佔之比例為50%、κ相所佔之比例為49%、γ相所佔之比例為1%時,α相中的Sn濃度約為0.15mass%,κ相中的Sn濃度約為0.22mass%,γ相中的Sn濃度約為1.8mass%。再者,若γ相的面積率大,則γ相中耗費之(消耗之)Sn的量增加,分佈於κ相、α相之Sn的量減少。因此,若γ相的量減少,則如後述那樣Sn有效地利用於耐蝕性、切削性中。 In the alloy of this embodiment, when the Sn content is 0.07 to 0.28 mass%, and when the amount of Sn distributed in the α phase is set to 1, Sn is about 1.4 in the κ phase and about 10 to about 17 in the γ phase. The ratio of about 2 to about 3 in the μ phase is distributed. By investing effort in the manufacturing process, the amount of distribution in the γ phase can be reduced to about 10 times the amount of distribution in the α phase. For example, in the case of the alloy of this embodiment, the proportion of α phase in a Cu-Zn-Si-Sn alloy containing Sn of 0.2 mass% is 50%, and the proportion of κ phase is 49% When the proportion of γ phase is 1%, the Sn concentration in the α phase is about 0.15 mass%, the Sn concentration in the κ phase is about 0.22 mass%, and the Sn concentration in the γ phase is about 1.8 mass%. Furthermore, if the area ratio of the γ phase is large, the amount of Sn consumed in the γ phase increases, and the amount of Sn distributed in the κ phase and the α phase decreases. Therefore, if the amount of the γ phase is reduced, as described later, Sn is effectively used for corrosion resistance and machinability.
另一方面,將分佈於α相之P量設為1時,P以於κ相中約2、於γ相中約3、於μ相中約3的比例被分佈。例如,在本實施形態的合金的情況下,在含有0.1mass%的P之Cu-Zn-Si合金中α相所佔之比例為50%、κ相所佔之比 例為49%、γ相所佔之比例為1%時,α相中的P濃度約為0.06mass%,κ相中的P濃度約為0.12mass%,γ相中的P濃度約為0.18mass%。 On the other hand, when the amount of P distributed in the α phase is set to 1, P is distributed at a ratio of about 2 in the κ phase, about 3 in the γ phase, and about 3 in the μ phase. For example, in the case of the alloy of this embodiment, the proportion of the α phase in the Cu-Zn-Si alloy containing 0.1 mass% of P is 50% and the ratio of the κ phase For example, when the ratio is 49% and the proportion of γ phase is 1%, the P concentration in the α phase is about 0.06 mass%, the P concentration in the κ phase is about 0.12 mass%, and the P concentration in the γ phase is about 0.18 mass. %.
Sn、P這兩者提高α相、κ相的耐蝕性,但與α相中所含之Sn、P的量相比,κ相中所含之Sn、P的量分別約1.4倍、約2倍。亦即,κ相中所含之Sn量為α相中所含之Sn量的約1.4倍,κ相中所含之P量為α相中所含之P量的約2倍。因此,κ相的耐蝕性的提高程度優於α相的耐蝕性的提高程度。其結果,κ相的耐蝕性接近α相的耐蝕性。再者,藉由一同添加Sn和P,尤其可提高κ相的耐蝕性,但包括含量的不同在內,Sn對耐蝕性的貢獻度大於P。 Both Sn and P improve the corrosion resistance of the α phase and the κ phase, but compared to the amounts of Sn and P contained in the α phase, the amounts of Sn and P contained in the κ phase are about 1.4 times and about 2 times, respectively. Times. That is, the amount of Sn contained in the κ phase is about 1.4 times the amount of Sn contained in the α phase, and the amount of P contained in the κ phase is about 2 times the amount of P contained in the α phase. Therefore, the degree of improvement in the corrosion resistance of the κ phase is superior to the degree of improvement in the corrosion resistance of the α phase. As a result, the corrosion resistance of the κ phase is close to that of the α phase. In addition, by adding Sn and P together, the corrosion resistance of the κ phase can be particularly improved. However, including the difference in content, the contribution of Sn to the corrosion resistance is greater than P.
當Sn的含量小於0.07mass%時,κ相的耐蝕性、耐脫鋅腐蝕性比α相的耐蝕性、耐脫鋅腐蝕性差,因此在惡劣的水質下,κ相有時會選擇性地被腐蝕。Sn在κ相中的較多分佈會提高耐蝕性比α相差之κ相的耐蝕性,使含有一定濃度以上的Sn之κ相的耐蝕性接近α相的耐蝕性。同時,在κ相中含有Sn時,提高κ相的切削性功能,並提高耐磨耗性。為此,κ相中的Sn濃度較佳為0.08mass%以上,更佳為0.11mass%以上,進一步較佳為0.14mass%以上。 When the content of Sn is less than 0.07 mass%, the corrosion resistance and dezincification resistance of the κ phase are inferior to that of the α phase and the dezincification corrosion resistance. Therefore, in poor water quality, the κ phase may be selectively corrosion. The more distribution of Sn in the κ phase will improve the corrosion resistance of the κ phase, which is worse than that of the α phase, and make the corrosion resistance of the κ phase containing Sn at a certain concentration more than that of the α phase. At the same time, when Sn is contained in the κ phase, the machinability of the κ phase is improved and the wear resistance is improved. Therefore, the Sn concentration in the κ phase is preferably 0.08 mass% or more, more preferably 0.11 mass% or more, and still more preferably 0.14 mass% or more.
另一方面,Sn大多分佈於γ相,但即使在γ相中 含有大量的Sn,亦主要由於γ相的結晶結構為BCC結構之理由,因而γ相的耐蝕性幾乎不會提高。不僅如此,若γ相所佔之比例較多,則分佈於κ相之Sn的量減少,因此κ相的耐蝕性提高的程度減小。若γ相的比例減小,則分佈於κ相之Sn的量增加。若κ相中分佈有大量的Sn,則κ相的耐蝕性、切削性能提高,從而能夠補償γ相的切削性的損失量。於κ相中含有規定量以上的Sn之結果,認為κ相自身的切削性功能、切屑的分割性能得到提高。其中,若κ相中的Sn濃度超過0.45mass%,則合金的切削性提高,但κ相的韌性開始受損。若進一步重視韌性,則κ相中的Sn濃度的上限較佳為0.45mass%以下,更佳為0.40mass%以下,進一步較佳為0.35mass%以下。 On the other hand, Sn is mostly distributed in the γ phase, but even in the γ phase Containing a large amount of Sn is also mainly due to the reason that the crystal structure of the γ phase is the BCC structure, so the corrosion resistance of the γ phase is hardly improved. Moreover, if the proportion of the γ phase is large, the amount of Sn distributed in the κ phase is reduced, and thus the degree of improvement in the corrosion resistance of the κ phase is reduced. When the proportion of the γ phase decreases, the amount of Sn distributed in the κ phase increases. If a large amount of Sn is distributed in the κ phase, the corrosion resistance and cutting performance of the κ phase are improved, and the loss of machinability of the γ phase can be compensated. As a result of containing more than a predetermined amount of Sn in the κ phase, it is considered that the machinability of the κ phase itself and the chip-splitting performance are improved. However, if the Sn concentration in the κ phase exceeds 0.45 mass%, the machinability of the alloy is improved, but the toughness of the κ phase begins to be impaired. If toughness is more important, the upper limit of the Sn concentration in the κ phase is preferably 0.45 mass% or less, more preferably 0.40 mass% or less, and still more preferably 0.35 mass% or less.
另一方面,若Sn的含量增加,則從與其他元素、Cu、Si之間的關係等考慮,減少γ相的量會變得困難。為了將γ相所佔之比例設為1.5%以下、進一步設為0.8%以下,需要將合金中的Sn的含量設為0.28mass%以下,將Sn的含量設為0.27mass%以下為較佳。 On the other hand, if the content of Sn is increased, it becomes difficult to reduce the amount of the γ phase in consideration of the relationship with other elements, Cu, and Si. In order to set the ratio of the γ phase to 1.5% or less and further 0.8% or less, it is necessary to set the Sn content in the alloy to 0.28 mass% or less, and it is preferable to set the Sn content to 0.27 mass% or less.
與Sn相同地,若P大多分佈於κ相,則耐蝕性提高並且有助於提高κ相的切削性。其中,當含有過量的P時,耗費在形成Si的金屬間化合物中而使特性變差,或者過量的P的固熔使衝擊特性和延展性受損。κ相中的P濃 度的下限值較佳為0.07mass%以上,更佳為0.08mass%以上。 κ相中的P濃度的上限值較佳為0.24mass%以下,更佳為0.20mass%以下,進一步較佳為0.16mass%以下。 As with Sn, if P is mostly distributed in the κ phase, the corrosion resistance is improved and the machinability of the κ phase is improved. Among them, when excessive P is contained, it is consumed in the Si-forming intermetallic compound to deteriorate the characteristics, or excessive solid solution melting impairs the impact characteristics and ductility. P concentration in κ phase The lower limit of the degree is preferably 0.07 mass% or more, and more preferably 0.08 mass% or more. The upper limit of the P concentration in the κ phase is preferably 0.24 mass% or less, more preferably 0.20 mass% or less, and still more preferably 0.16 mass% or less.
<特性> <Features>
(常溫強度及高溫強度) (Normal temperature strength and high temperature strength)
作為包括飲用水的閥、器具、汽車在內的各種領域中所需的強度,適用於壓力容器之裂斷應力(breaking stress)之抗拉強度視為重要。又,例如在靠近汽車的發動機室之環境下使用之閥或高溫/高壓閥,於最高150℃的溫度環境下使用,但此時當然會要求在施加有應力時不會變形或被破壞。在壓力容器的情況下,其容許應力影響抗拉強度。 As strength required in various fields including valves, appliances, and automobiles for drinking water, tensile strength suitable for the breaking stress of a pressure vessel is considered important. In addition, for example, a valve or a high-temperature / high-pressure valve used in an environment close to the engine room of a car is used in a temperature environment up to 150 ° C. However, it is of course required that the valve is not deformed or damaged when stress is applied. In the case of a pressure vessel, its allowable stress affects the tensile strength.
為此,作為熱加工材料之熱擠出材料及熱鍛造材料,係常溫下的抗拉強度為530N/mm2以上之高強度材料為較佳。常溫下的抗拉強度較佳為550N/mm2以上。實質上,熱鍛造材料一般不實施冷加工。 For this reason, as a hot-extruded material and a hot-forged material of a hot working material, a high-strength material having a tensile strength of 530 N / mm 2 or more at normal temperature is preferable. The tensile strength at room temperature is preferably 550 N / mm 2 or more. In essence, hot forging materials are generally not cold worked.
另一方面,在某些情況下,熱加工材料被冷拉伸、拉線而強度提高。本實施形態的合金中,在實施冷加工的情況下冷加工率為15%以下時,冷加工率每上升1%,抗拉強度上升約12N/mm2。相反,冷加工率每減少1%,衝擊特性減少約4%或5%。例如,當對抗拉強度為560N/mm2、衝擊值為30J/cm2的合金材料實施冷加工率5%的冷拉伸來製作 冷加工材料時,冷加工材料的抗拉強度約為620N/mm2,衝擊值約成為23J/cm2。若冷加工率不同,則抗拉強度、衝擊值不能唯一確定。 On the other hand, in some cases, the strength of the hot-worked material is increased by cold drawing or drawing. In the alloy according to this embodiment, when the cold working ratio is 15% or less when cold working is performed, each 1% increase in the cold working ratio increases the tensile strength by about 12 N / mm 2 . In contrast, for every 1% reduction in cold working rate, the impact characteristics are reduced by about 4% or 5%. For example, when an alloy material with a tensile strength of 560 N / mm 2 and an impact value of 30 J / cm 2 is subjected to cold drawing at a cold working rate of 5% to produce a cold-worked material, the cold-worked material has a tensile strength of about 620 N / mm 2 , The impact value is approximately 23 J / cm 2 . If the cold working rates are different, the tensile strength and impact value cannot be uniquely determined.
另一方面,當進行拉伸、拉線之冷加工、繼而實施適當條件的熱處理時,與熱擠出材料相比,抗拉強度、衝擊特性均提高。藉由冷加工,強度提高,衝擊特性降低。藉由熱處理,γ相減少,κ相的比例增加,於α相內存在針狀κ相。又,基地的α相、κ相得到恢復。藉此,與熱擠出材料相比,耐蝕性、抗拉強度、衝擊值均大幅提高,被製成更高強度且高韌性的合金。 On the other hand, when drawing, cold working of a wire, and subsequent heat treatment under appropriate conditions, both tensile strength and impact characteristics are improved compared to hot extruded materials. By cold working, the strength is increased and the impact characteristics are reduced. By heat treatment, the γ phase decreases and the proportion of the κ phase increases, and a needle-like κ phase exists in the α phase. The α and κ phases of the base were restored. As a result, compared with hot extrusion materials, corrosion resistance, tensile strength, and impact value are greatly improved, and alloys with higher strength and toughness are made.
關於高溫強度,在負載有相當於室溫的0.2%保證應力之應力的狀態下,於150℃將銅合金保持100小時後的潛變應變係0.4%以下為較佳。該潛變應變更佳為0.3%以下,進一步較佳為0.2%以下。該情況下,即使如高溫高壓閥、靠近汽車的發動機室的閥材料等那樣曝露於高溫下,亦不易變形,高溫強度優異。 Regarding the high temperature strength, it is preferable that the latent strain system after holding the copper alloy at 150 ° C for 100 hours under a stress equivalent to 0.2% of the guaranteed stress at room temperature is 0.4% or less. This creep change should preferably be 0.3% or less, and more preferably 0.2% or less. In this case, even if exposed to a high temperature such as a high-temperature and high-pressure valve, a valve material close to an engine room of an automobile, etc., it is not easily deformed and has excellent high-temperature strength.
另外,在含有60mass%的Cu、3mass%的Pb且剩餘部分包括Zn及不可避免的雜質之含Pb之易削黃銅的情況下,熱擠出材料、熱鍛造品在常溫下的抗拉強度為360N/mm2~400N/mm2。又,即使在負載有相當於室溫的0.2%保證應力之應力之狀態下,將合金於150℃曝露100 小時之後,潛變應變亦約為4~5%。因此,與現有的含有Pb之易削黃銅相比,本實施形態的合金的抗拉強度、耐熱性為較高水準。亦即,本實施形態的合金在室溫下具備高強度,即使附加該高強度而長時間曝露於高溫下亦幾乎不變形,因此能夠利用高強度來實現薄壁化/輕量化。尤其在高壓閥等鍛造材料的情況下無法實施冷加工,因此藉由利用高強度來實現高性能、薄壁化及輕量化。 In addition, the tensile strength of hot extruded materials and hot-forged products at room temperature in the case of free-cutting brasses containing 60 mass% Cu and 3 mass% Pb and the rest including Zn and unavoidable impurities containing Pb 360N / mm 2 to 400N / mm 2 . In addition, even when the alloy is loaded with a stress equivalent to 0.2% of the guaranteed stress at room temperature, after exposing the alloy at 150 ° C for 100 hours, the creep strain is about 4 to 5%. Therefore, compared with the conventional free-cutting brass containing Pb, the tensile strength and heat resistance of the alloy of this embodiment are higher. That is, the alloy of the present embodiment has high strength at room temperature, and hardly deforms even if it is exposed to high temperature for a long period of time when the high strength is added. Therefore, thinning and weight reduction can be achieved by high strength. In particular, in the case of forged materials such as high-pressure valves, cold working cannot be performed. Therefore, high strength is used to achieve high performance, thinning, and weight reduction.
本實施形態的合金的高溫特性對於擠出材料、實施了冷加工之材料亦大致相同。亦即,藉由實施冷加工,0.2%保證應力提高,但即使在施加了相當於較高的0.2%保證應力之荷載之狀態下,將合金於150℃曝露100小時之後的潛變應變亦為0.4%以下且具備高耐熱性。高溫特性主要影響β相、γ相、μ相的面積率,面積率越高,該高溫特性變得越差。又,存在於α相的晶粒邊界和相邊界之μ相、γ相的長邊的長度越長越,該高溫特性變得越差。 The high-temperature characteristics of the alloy of this embodiment are also substantially the same for extruded materials and materials subjected to cold working. That is, by implementing cold working, the 0.2% guaranteed stress is increased, but even when a load equivalent to a higher 0.2% guaranteed stress is applied, the creep strain of the alloy after exposure to 150 ° C for 100 hours is 0.4. % Or less and has high heat resistance. The high temperature characteristics mainly affect the area ratios of the β phase, the γ phase, and the μ phase. The higher the area ratio, the worse the high temperature characteristics become. Further, as the lengths of the long sides of the μ phase and the γ phase existing at the grain boundaries and phase boundaries of the α phase become longer, the high temperature characteristics become worse.
(耐衝擊性) (Impact resistance)
通常,在材料具有高強度時變脆。在切削時切屑的分割性優異之材料被認為具有某種脆性。衝擊特性與切削性和強度在某些方面是矛盾之特性。 Generally, it becomes brittle when the material has high strength. A material that is excellent in chip separation during cutting is considered to have some kind of brittleness. Impact characteristics are contradictory to machinability and strength in some respects.
然而,當銅合金使用於閥、接頭、閥等飲用水器具、汽車組件、機械組件、工業用配管等各種構件時,銅合金 不僅需要為高強度,還需要耐衝擊之特性。具體而言,用U形凹口試片進行夏比衝擊試驗時,夏比衝擊試驗值較佳為超過14J/cm2,更佳為17J/cm2以上。尤其,關於未實施冷加工的熱鍛材料、擠出材料等各熱處理材料,用U形凹口試片進行夏比衝擊試驗時,夏比衝擊試驗值較佳為17J/cm2以上,更佳為20J/cm2以上,進一步較佳為24J/cm2以上。本實施形態的合金係關於切削性優異之合金,即使考慮到用途,亦不需要夏比衝擊試驗值超過50J/cm2。若夏比衝擊試驗值超過50J/cm2,則韌性反而增加,因此切削阻力增大,切屑變得容易連接等切削性變差。因此,夏比衝擊試驗值較佳為小於50J/cm2。 However, when copper alloys are used in various components such as drinking water appliances such as valves, joints, and valves, automotive components, mechanical components, and industrial piping, copper alloys need not only high strength but also impact resistance. Specifically, when a Charpy impact test with U-shaped recess oral tablets, Charpy impact value is preferably more than 14J / cm 2, more preferably 17J / cm 2 or more. In particular, for each heat-treated material such as hot-forged materials and extruded materials that have not been cold-worked, when a Charpy impact test is performed using a U-shaped notch test piece, the Charpy impact test value is preferably 17 J / cm 2 or more, and more preferably 20 J / cm 2 or more, and more preferably 24 J / cm 2 or more. The alloy of this embodiment is an alloy having excellent machinability, and even if the application is considered, the Charpy impact test value does not need to exceed 50 J / cm 2 . If the Charpy impact test value exceeds 50 J / cm 2 , the toughness will increase on the contrary, so the cutting resistance will increase, and the chipability will be deteriorated, such as the chips becoming easier to connect. Therefore, the Charpy impact test value is preferably less than 50 J / cm 2 .
若硬質的κ相增加或κ相中的Sn濃度變高,則強度、切削性提高,但韌性亦即衝擊特性降低。因此,強度和切削性與韌性(衝擊特性)為矛盾之特性。藉由下式定義強度中摻加了衝擊特性之強度指數。 When the hard κ phase is increased or the Sn concentration in the κ phase is increased, the strength and machinability are improved, but the toughness, that is, the impact characteristics is decreased. Therefore, strength, machinability, and toughness (impact characteristics) are contradictory characteristics. The strength index with impact characteristics added to the strength is defined by the following formula.
(強度指數)=(抗拉強度)+25×(夏比衝擊值)1/2 (Strength Index) = (tensile strength) + 25 × (Charpy impact value) 1/2
關於熱加工材料(熱擠出材料、熱鍛材料)及實施了加工率約為10%左右的輕度冷加工之冷加工材料,若強度指數為670以上,則可以說係高強度且具備韌性之材料。 強度指數較佳為680以上,更佳為690以上。 Regarding hot-worked materials (hot-extruded materials, hot-forged materials) and cold-worked materials that have undergone mild cold working with a processing rate of about 10%, if the strength index is 670 or more, it can be said that they are high-strength and tough materials . The strength index is preferably 680 or more, and more preferably 690 or more.
衝擊特性與金相組織有密切的關係,γ相使衝擊特 性變差。又,若μ相存在於α相的晶粒邊界、α相、κ相、γ相的相邊界,則晶粒邊界及相邊界變脆而衝擊特性變差。 The impact characteristics are closely related to the metallographic structure, and the γ phase makes the impact particularly Sexual deterioration. In addition, if the μ phase exists at the grain boundary of the α phase, the phase boundary of the α phase, the κ phase, and the γ phase, the grain boundary and the phase boundary become brittle and the impact characteristics deteriorate.
研究結果得到,若在晶粒邊界、相邊界存在長邊的長度超過25μm之μ相,則衝擊特性尤其變差。因此,所存在之μ相的長邊的長度為25μm以下,較佳為15μm以下,更佳為5μm以下,最佳為2μm以下。又,同時與α相和κ相相比,存在於晶粒邊界之μ相在惡劣環境下容易被腐蝕而產生晶界腐蝕,並且使高溫特性變差。 As a result of the study, it was found that if a μ phase having a longer side length of more than 25 μm exists at the grain boundary and the phase boundary, the impact characteristics are particularly deteriorated. Therefore, the length of the long side of the existing μ phase is 25 μm or less, preferably 15 μm or less, more preferably 5 μm or less, and most preferably 2 μm or less. In addition, compared with the α phase and the κ phase, the μ phase existing at the grain boundary is easily corroded in a severe environment to cause grain boundary corrosion, and deteriorates the high temperature characteristics.
再者,在μ相的情況下,若其佔有比例減小,且μ相的長度較短,寬度變窄,則在500倍或1000倍左右倍率的金屬顯微鏡中變得難以確認。當μ相的長度為5μm以下時,若用倍率為2000倍或5000倍的電子顯微鏡進行觀察,則有時能夠在晶粒邊界、相邊界觀察μ相。 Furthermore, in the case of the μ phase, if the occupation ratio is reduced, and the length of the μ phase is short and the width is narrowed, it becomes difficult to confirm in a metal microscope with a magnification of about 500 or 1000 times. When the length of the μ phase is 5 μm or less, when observed with an electron microscope with a magnification of 2000 or 5000, the μ phase may sometimes be observed at the grain boundaries and phase boundaries.
<製造製程> <Manufacturing process>
接著,對本發明的第1、2實施形態之易削性銅合金的製造方法進行說明。 Next, a method for manufacturing a free-cutting copper alloy according to the first and second embodiments of the present invention will be described.
本實施形態的合金的金相組織不僅在組成中發生變化,而且在製造製程中亦發生變化。不僅影響熱擠壓、熱鍛造的熱加工溫度、熱處理溫度和熱處理條件,而且熱加工和熱處理的冷卻過程中的平均冷卻速度亦受到影響。進行深入研究之結果得知,在熱加工和熱處理的冷卻過程 中,金相組織較大影響在470℃至380℃的溫度區域的冷卻速度及在575℃至510℃尤其在570℃至530℃的溫度區域的平均冷卻速度。 The metallographic structure of the alloy of this embodiment changes not only in the composition but also in the manufacturing process. Not only affects the hot working temperature, heat treatment temperature and heat treatment conditions of hot extrusion, hot forging, but also the average cooling rate during the cooling process of hot work and heat treatment. As a result of in-depth research, the cooling process in hot working and heat treatment was learned In the metallographic structure, the cooling rate in the temperature range of 470 ° C to 380 ° C and the average cooling rate in the temperature range of 575 ° C to 510 ° C, especially 570 ° C to 530 ° C are greatly affected.
本實施形態的製造製程對本實施形態的合金而言為必要的製程,具有與組成的平衡,但基本發揮以下重要效果。 The manufacturing process of this embodiment is a necessary process for the alloy of this embodiment, and has a balance with the composition, but basically exhibits the following important effects.
1)減少使耐蝕性、衝擊特性變差之γ相,並減小γ相的長邊的長度。 1) Reduce the γ phase which deteriorates the corrosion resistance and impact characteristics, and reduce the length of the long side of the γ phase.
2)控制使耐蝕性、衝擊特性變差之μ相,並控制μ相的長邊的長度。 2) Control the μ phase that deteriorates the corrosion resistance and impact characteristics, and control the length of the long side of the μ phase.
3)使針狀κ相析出於α相內。 3) The needle-like κ phase is separated into the α phase.
4)藉由減少γ相的量並且減少固熔於γ相之Sn的量來增加固熔於κ相和α相之Sn的量(濃度)。 4) The amount (concentration) of Sn solidified in the κ phase and the α phase is increased by reducing the amount of the γ phase and reducing the amount of Sn solidified in the γ phase.
(熔解鑄造) (Melting Casting)
熔解在比本實施形態的合金的熔點(液相線溫度)高約100℃~約300℃的溫度亦即約950℃~約1200℃進行。 鑄造在比熔點高約50℃~約200℃的溫度亦即約900℃~約1100℃進行。澆鑄於規定的鑄模中,並藉由氣冷、緩冷卻、水冷等幾種冷卻方式來進行冷卻。而且,凝固後,構成相發生各種變化。 The melting is performed at a temperature of about 100 ° C to about 300 ° C, that is, about 950 ° C to about 1200 ° C, which is higher than the melting point (liquidus temperature) of the alloy of this embodiment. Casting is performed at a temperature about 50 ° C to about 200 ° C higher than the melting point, that is, about 900 ° C to about 1100 ° C. It is cast into a predetermined mold, and is cooled by several cooling methods such as air cooling, slow cooling, and water cooling. In addition, after solidification, various changes occur in the constituent phases.
(熱加工) (Thermal processing)
作為熱加工,可舉出熱擠壓、熱鍛造。 Examples of the hot working include hot extrusion and hot forging.
關於熱擠壓,雖然依設備能力而不同,但在實際進行熱加工時的材料溫度、具體而言剛通過擠出模後的溫度(熱加工溫度)為600~740℃之條件下實施熱擠壓為較佳。若在超過740℃之溫度進行熱加工,則在塑性加工時形成許多β相,有時β相會殘留,γ相亦有較多殘留,從而對冷卻後的構成相產生不良影響。又,即使在下一製程中實施熱處理,亦影響熱加工材料的金相組織。具體而言,與在740℃以下的溫度進行熱加工時相比,在超過740℃之溫度實施熱加工時,γ相變多,或者在某些情況下β相殘留或發生熱加工破裂。再者,熱加工溫度為670℃以下為較佳,645℃以下為更佳。若於645℃以下實施熱擠壓,則熱擠出材料的γ相減少。當對該熱擠出材料接著實施熱鍛造和熱處理而製作熱鍛材料、熱處理材料時,熱鍛材料、熱處理材料的γ相的量變得更少。 Regarding hot extrusion, although it differs depending on the equipment capacity, the hot extrusion is carried out under the condition that the material temperature during the actual hot working, specifically the temperature immediately after passing through the extrusion die (hot working temperature) is 600 to 740 ° C Pressing is better. If the hot working is performed at a temperature exceeding 740 ° C, many β phases are formed during plastic working, and sometimes the β phase may remain and the γ phase may remain more, thereby adversely affecting the constituent phases after cooling. Moreover, even if heat treatment is performed in the next process, the metallographic structure of the hot-worked material is affected. Specifically, compared with the case where hot working is performed at a temperature of 740 ° C. or less, when the hot working is performed at a temperature exceeding 740 ° C., the γ phase becomes larger, or in some cases the β phase remains or thermal processing cracking occurs. The hot working temperature is preferably 670 ° C or lower, and more preferably 645 ° C or lower. When hot extrusion is performed at 645 ° C or lower, the γ phase of the hot-extruded material decreases. When the hot extruded material is subsequently subjected to hot forging and heat treatment to produce a hot forged material or a heat treated material, the amount of the γ phase of the hot forged material or the heat treated material becomes smaller.
而且,進行冷卻時,將在470℃至380℃的溫度區域的平均冷卻速度設為超過2.5℃/分鐘且小於500℃/分鐘。在470℃至380℃的溫度區域的平均冷卻速度,較佳為4℃/分鐘以上,更佳為8℃/分鐘以上。藉此,防止μ相增加。 When cooling is performed, the average cooling rate in a temperature range of 470 ° C to 380 ° C is set to exceed 2.5 ° C / min and less than 500 ° C / min. The average cooling rate in a temperature range of 470 ° C to 380 ° C is preferably 4 ° C / min or more, and more preferably 8 ° C / min or more. This prevents an increase in the μ phase.
又,當熱加工溫度較低時,熱下的變形阻力增大。從變形能力方面考慮,熱加工溫度的下限較佳為600℃以上,更佳為605℃以上。當擠出比為50以下時或熱鍛造成比較 簡單的形狀時,能夠於600℃以上實施熱加工。若考慮裕度,熱加工溫度的下限較佳為605℃。雖然依設備能力而不同,但從金相組織的構成相的觀點考慮,熱加工溫度儘可能低為較佳。 When the hot working temperature is low, the deformation resistance under heat increases. From the viewpoint of deformability, the lower limit of the hot working temperature is preferably 600 ° C or higher, and more preferably 605 ° C or higher. When the extrusion ratio is 50 or less or compared by hot forging For simple shapes, hot working can be performed at 600 ° C or higher. In consideration of the margin, the lower limit of the hot working temperature is preferably 605 ° C. Although it differs depending on the equipment capability, it is preferable that the hot working temperature is as low as possible from the viewpoint of the constituent phase of the metallographic structure.
考慮可實測的測定位置,熱加工溫度定義為熱擠壓或熱鍛造後約3秒後的可實測的熱加工材料的溫度。金相組織受剛受到大塑性變形之加工後的溫度影響。 Considering the measurable measurement position, the hot working temperature is defined as the temperature of the measurable hot working material after about 3 seconds after hot extrusion or hot forging. The metallurgical structure is affected by the temperature just after the large plastic deformation.
含有1~4mass%的量的Pb之黃銅合金佔銅合金擠出材料的絕大部分,在該黃銅合金的情況下,除了擠出直徑大者、例如直徑約超過38mm者以外,通常在熱擠壓後捲繞成線圈。擠出的鑄錠(小坯)被擠出裝置奪去熱量從而溫度降低。擠出材料藉由與捲繞裝置接觸而被奪去熱量,從而溫度進一步降低。從最初擠出的鑄錠溫度,或從擠出材料的溫度,以比較快的平均冷卻速度發生約50℃~100℃的溫度下降。之後,捲繞之線圈藉由保溫效果,雖然依線圈的重量等而不同,但以約2℃/分鐘的比較慢的平均冷卻速度在470℃至380℃的溫度區域進行冷卻。當材料溫度達到約300℃時,其之後的平均冷卻速度進一步變慢,因此有時會考慮到處理而進行水冷。在含有Pb之黃銅合金的情況下,以約600~800℃進行熱擠壓,但剛擠出後的金相組織中存在大量的富有熱加工性之β相。若擠出後的平均冷 卻速度快,則冷卻後的金相組織中殘留大量的β相,從而耐蝕性、延展性、衝擊特性、高溫特性變差。為了避免該種情況,以利用了擠出線圈的保溫效果等之比較慢的平均冷卻速度進行冷卻,藉此使β相變為α相,從而成為富含α相之金相組織。如前述,剛擠出後,擠出材料的平均冷卻速度比較快,因此藉由減緩之後的冷卻而成為富含α相之金相組織。再者,專利文獻1中雖然沒有關於平均冷卻速度的記載,但揭示了為了減少β相並使β相孤立,進行緩冷卻直至擠出材料的溫度成為180℃以下。 A brass alloy containing Pb in an amount of 1 to 4 mass% accounts for most of the copper alloy extruded material. In the case of the brass alloy, in addition to extruding a larger diameter, for example, a diameter exceeding about 38 mm, it is usually It is wound into a coil after hot extrusion. The extruded ingot (small billet) is deprived of heat by the extruder and the temperature is reduced. The extruded material is deprived of heat by contact with the winding device, thereby further reducing the temperature. From the temperature of the ingot that was initially extruded, or from the temperature of the extruded material, a temperature drop of about 50 ° C to 100 ° C occurs at a relatively fast average cooling rate. After that, the wound coil is cooled in a temperature range of 470 ° C to 380 ° C at a relatively slow average cooling rate of about 2 ° C / minute, although the winding coil has a thermal insulation effect, which varies depending on the weight of the coil. When the temperature of the material reaches about 300 ° C, the average cooling rate thereafter becomes further slower, and therefore, water cooling may be performed in consideration of processing. In the case of a brass alloy containing Pb, hot extrusion is performed at about 600 to 800 ° C, but there are a large number of β phases rich in hot workability in the metallurgical structure immediately after extrusion. If the average cold after extrusion However, if the speed is high, a large amount of β phases remain in the cooled metallurgical structure, and the corrosion resistance, ductility, impact characteristics, and high temperature characteristics are deteriorated. In order to avoid such a situation, the cooling is performed at a relatively slow average cooling rate using the heat preservation effect of the extruded coil, etc., thereby changing the β phase to the α phase, thereby becoming a metallographic structure rich in the α phase. As mentioned above, the average cooling rate of the extruded material is relatively fast immediately after extrusion, so it becomes a metallographic structure rich in α phase by slowing down the subsequent cooling. Further, although there is no description of the average cooling rate in Patent Document 1, it is disclosed that in order to reduce the β phase and isolate the β phase, the cooling is slowly performed until the temperature of the extruded material becomes 180 ° C or lower.
如上所述,以與現有的含有Pb之黃銅合金的製造方法完全不同之冷卻速度來製造本實施形態的合金。 As described above, the alloy of this embodiment is produced at a cooling rate that is completely different from the conventional method for producing a brass alloy containing Pb.
(熱鍛造) (Hot forged)
作為熱鍛造的原材料主要使用熱擠出材料,但亦可以使用連續鑄造棒。與熱擠壓相比,熱鍛造中加工成複雜的形狀,因此鍛造前的原材料的溫度較高。但是,成為鍛造品的主要部位之施加有大塑性加工之熱鍛造材料的溫度亦即自鍛造後約3秒後的材料溫度與擠出材料相同係600℃至740℃為較佳。 As a raw material for hot forging, a hot extrusion material is mainly used, but a continuous casting rod may also be used. Compared with hot extrusion, hot forging processes into complex shapes, so the temperature of the raw materials before forging is higher. However, the temperature of the hot forged material to which large plastic working is applied, which is the main part of the forged product, that is, the material temperature about 3 seconds after forging is the same as that of the extruded material, which is 600 ° C to 740 ° C.
再者,只要降低製造熱擠壓棒時的擠壓溫度,並設為γ相少的金相組織,則在對該熱擠壓棒實施熱鍛造時,即使熱鍛溫度高,亦可以得到γ相少的熱鍛組織。 In addition, as long as the extrusion temperature at the time of manufacturing the hot extruded rod is reduced, and the metallographic structure has a small amount of γ phase, when hot forging is performed on the hot extruded rod, γ can be obtained even if the hot forging temperature is high. Relatively few hot forged structures.
此外,藉由在鍛造後的平均冷卻速度上花費精力,能夠得到具備耐蝕性、切削性等各種特性之材料。亦即,在熱鍛造後經過3秒之時點的鍛造材料的溫度為600℃以上740℃以下。在之後的冷卻過程中,若在575℃至510℃的溫度區域,尤其在570℃至530℃的溫度區域中,若以0.1℃/分鐘以上且2.5℃/分鐘以下的平均冷卻速度進行冷卻,則γ相減少。考慮到經濟性,將在575℃至510℃的溫度區域的平均冷卻速度的下限值設為0.1℃/分鐘以上,若平均冷卻速度超過2.5℃/分鐘,則γ相的量的減少變得不充分。 該在575℃至510℃的溫度區域的平均冷卻速度,較佳為1.5℃/分鐘以下,更佳為1℃/分鐘以下。而且,將在470℃至380℃的溫度區域的平均冷卻速度設為超過2.5℃/分鐘且小於500℃/分鐘。在470℃至380℃的溫度區域的平均冷卻速度,較佳為4℃/分鐘以上,更佳為8℃/分鐘以上。 藉此,防止μ相增加。這樣,在575~510℃的溫度區域中,以2.5℃/分鐘以下,較佳為1.5℃/分鐘以下的平均冷卻速度進行冷卻。又,在470至380℃的溫度區域中,以超過2.5℃/分鐘,較佳為4℃/分鐘以上的平均冷卻速度進行冷卻。這樣,在575~510℃的溫度區域中減緩平均冷卻速度,在470至380℃的溫度區域中相反地加快平均冷卻速度,藉此製成更合適的材料。 In addition, by devoting effort to the average cooling rate after forging, a material having various characteristics such as corrosion resistance and machinability can be obtained. That is, the temperature of the forged material at the point of 3 seconds after hot forging is 600 ° C or higher and 740 ° C or lower. In the subsequent cooling process, if in the temperature range of 575 ° C to 510 ° C, especially in the temperature range of 570 ° C to 530 ° C, if the average cooling rate is 0.1 ° C / min or more and 2.5 ° C / min or less, Then the γ phase decreases. In consideration of economy, the lower limit value of the average cooling rate in a temperature range of 575 ° C to 510 ° C is set to 0.1 ° C / min or more. If the average cooling rate exceeds 2.5 ° C / min, the amount of the γ phase decreases. insufficient. The average cooling rate in the temperature range of 575 ° C to 510 ° C is preferably 1.5 ° C / min or less, and more preferably 1 ° C / min or less. Moreover, the average cooling rate in a temperature range of 470 ° C to 380 ° C is set to exceed 2.5 ° C / min and less than 500 ° C / min. The average cooling rate in a temperature range of 470 ° C to 380 ° C is preferably 4 ° C / min or more, and more preferably 8 ° C / min or more. This prevents an increase in the μ phase. Thus, in the temperature range of 575 to 510 ° C, cooling is performed at an average cooling rate of 2.5 ° C / minute or less, preferably 1.5 ° C / minute or less. In the temperature range of 470 to 380 ° C, cooling is performed at an average cooling rate exceeding 2.5 ° C / minute, preferably 4 ° C / minute or more. In this way, the average cooling rate is slowed down in the temperature range of 575 to 510 ° C, and the average cooling rate is reversedly accelerated in the temperature range of 470 to 380 ° C, thereby making a more suitable material.
(冷加工製程) (Cold working process)
為了提高尺寸精度,或為了使擠出之線圈成為直線,亦可以對熱擠出材料實施冷加工。詳細而言,針對熱擠出材料或熱處理材料,以約2%~約20%(較佳約為2%~約15%,更佳約為2%~約10%)的加工率實施冷拉伸,然後進行矯正(複合拉伸、矯正)。或者,針對熱擠出材料或熱處理材料,以約2%~約20%(較佳約為2%~約15%,更佳約為2%~約10%)的加工率實施冷拉線加工。再者,冷加工率大致為0%,但有時僅藉由矯正設備來提高棒材的線性度。 In order to improve the dimensional accuracy or to make the extruded coils straight, it is also possible to cold process the hot extruded material. In detail, cold drawing is performed on a hot extrusion material or a heat-treated material at a processing rate of about 2% to about 20% (preferably about 2% to about 15%, more preferably about 2% to about 10%). Stretch and then correct (compound stretching, correction). Or, for hot extruded materials or heat-treated materials, cold drawing is performed at a processing rate of about 2% to about 20% (preferably about 2% to about 15%, more preferably about 2% to about 10%). . In addition, although the cold working rate is approximately 0%, the linearity of the bar is sometimes improved only by the correction equipment.
(熱處理(退火)) (Heat treatment (annealing))
就熱處理而言,例如在熱擠壓中加工成無法擠出的小尺寸時,在冷拉伸或冷拉線後依需要而實施熱處理,並使其再結晶亦即使材料變軟。又,在熱加工材料中,亦在如需要幾乎沒有加工應變的材料時或設為適當的金相組織時,依需要而在熱加工後實施熱處理。 In terms of heat treatment, for example, when processing into a small size that cannot be extruded during hot extrusion, heat treatment is performed after cold drawing or cold drawing as needed, and the material is recrystallized even if it becomes soft. In addition, in the case of a hot-worked material, when a material having almost no processing strain is required or when an appropriate metallographic structure is required, a heat treatment is performed after hot working as necessary.
在含有Pb之黃銅合金中,亦依需要而實施熱處理。在專利文獻1的含有Bi之黃銅合金的情況下,在350~550℃、1~8小時的條件下進行熱處理。 In brass alloys containing Pb, heat treatment is also performed as needed. In the case of a brass alloy containing Bi in Patent Document 1, heat treatment is performed at a temperature of 350 to 550 ° C. for 1 to 8 hours.
在本實施形態的合金的情況下,若在510℃以上且575℃以下的溫度保持20分鐘以上且8小時以下,則耐蝕性、 衝擊特性、高溫特性提高。但是,若在材料的溫度超過620℃之條件下進行熱處理,則反而形成許多γ相或β相,並使α相變得粗大。作為熱處理條件,熱處理的溫度係575℃以下為佳,570℃以下為較佳。在低於510℃的溫度的熱處理中,γ相的減少略有停止,並出現μ相。因此,熱處理的溫度較佳為510℃以上,更佳為530℃以上。熱處理的時間(以熱處理的溫度保持之時間)需要在510℃以上且575℃以下的溫度至少保持20分鐘以上。保持時間有助於減少γ相,因此保持時間較佳為30分鐘以上,更佳為50分鐘以上,最佳為80分鐘以上。從經濟性考慮,保持時間的上限為480分鐘以下,較佳為240分鐘以下。 In the case of the alloy of this embodiment, if it is maintained at a temperature of 510 ° C or higher and 575 ° C or lower for 20 minutes or more and 8 hours or less, the corrosion resistance, Improved impact and high temperature characteristics. However, if the heat treatment is performed under the condition that the temperature of the material exceeds 620 ° C., many γ phases or β phases are formed instead, and the α phase becomes coarse. As the heat treatment conditions, the heat treatment temperature is preferably 575 ° C or lower, and more preferably 570 ° C or lower. In the heat treatment at a temperature lower than 510 ° C, the reduction of the γ phase stopped slightly, and the μ phase appeared. Therefore, the temperature of the heat treatment is preferably 510 ° C or higher, and more preferably 530 ° C or higher. The heat treatment time (the time for which the heat treatment temperature is maintained) needs to be maintained at a temperature of 510 ° C or higher and 575 ° C or lower for at least 20 minutes. The holding time helps reduce the γ phase, so the holding time is preferably 30 minutes or more, more preferably 50 minutes or more, and most preferably 80 minutes or more. In terms of economy, the upper limit of the holding time is 480 minutes or less, and preferably 240 minutes or less.
再者,熱處理的溫度係530℃以上且570℃以下為較佳。 與530℃以上且570℃以下的熱處理相比,在510℃以上且小於530℃的熱處理的情況下,為了減少γ相,需要2倍或3倍以上的熱處理時間。 The temperature of the heat treatment is preferably 530 ° C or higher and 570 ° C or lower. Compared with heat treatment at 530 ° C or higher and 570 ° C or lower, in the case of heat treatment at 510 ° C or higher and less than 530 ° C, in order to reduce the γ phase, a heat treatment time of 2 times or 3 times is required.
藉由熱處理的時間(t)(分鐘)和熱處理的溫度(T)(℃)來定義由以下數式所表示之熱處理之值。 The value of the heat treatment represented by the following formula is defined by the time (t) (minutes) of the heat treatment and the temperature (T) (° C) of the heat treatment.
(熱處理之值)=(T-500)×t (Value of heat treatment) = (T-500) × t
其中,T為540℃以上時設為540。 It should be noted that when T is 540 ° C or higher.
上述熱處理之值係800以上為較佳,係1200以上為更佳。 The value of the heat treatment is preferably 800 or more, and more preferably 1200 or more.
如前述,利用熱擠壓和熱鍛造後的高溫狀態,藉由在平均冷卻速度上花費精力,在相當於在510℃以上且575℃以下的溫度區域中保持20分鐘以上之條件下,亦即在冷卻過程中在575℃至510℃的溫度區域以0.1℃/分鐘以上且2.5℃/分鐘以下的平均冷卻速度進行冷卻,藉此能夠改善金相組織。在575℃至510℃的溫度區域以2.5℃/分鐘以下進行冷卻的情況與在510℃以上且575℃以下的溫度區域中保持20分鐘的情況,在時間上大致相同。簡單計算時,成為以510℃以上且575℃以下的溫度加熱26分鐘的情況。 平均冷卻速度較佳為1.5℃/分鐘以下,更佳為1℃/分鐘以下。考慮到經濟性,則平均冷卻速度的下限設為0.1℃/分鐘以上。 As described above, by using the high-temperature state after hot extrusion and hot forging, and spending energy on the average cooling rate, it is maintained for a period of more than 20 minutes in a temperature range equivalent to 510 ° C or higher and 575 ° C or lower, that is, During the cooling process, the metallographic structure can be improved by cooling in a temperature range of 575 ° C to 510 ° C at an average cooling rate of 0.1 ° C / minute or more and 2.5 ° C / minute or less. The case where cooling is performed at a temperature of 2.5 ° C./min or less in a temperature range of 575 ° C. to 510 ° C. is substantially the same as the case of holding for 20 minutes in a temperature range of 510 ° C. or more and 575 ° C. or less. In a simple calculation, it is a case where it is heated at a temperature of 510 ° C or higher and 575 ° C or lower for 26 minutes. The average cooling rate is preferably 1.5 ° C / min or less, and more preferably 1 ° C / min or less. In consideration of economy, the lower limit of the average cooling rate is set to 0.1 ° C / min or more.
作為另一個熱處理方法,當在熱擠出材料、熱鍛造品或冷拉伸、拉線之材料在熱源內移動之連續熱處理爐的情況下,若超過620℃,則為如前述的問題。但是,藉由暫且將材料的溫度提升至575℃以上且620℃以下,繼而在相當於在510℃以上且575℃以下的溫度區域中保持20分鐘以上之條件下,亦即在510℃以上且575℃以下的溫度區域以0.1℃/分鐘以上且2.5℃/分鐘以下的平均冷卻速度進行冷卻,藉此能夠改善金相組織。在575℃至510℃的溫度區域的平均冷卻速度,較佳為2℃/分鐘以下,更佳為1.5℃/ 分鐘以下,進一步較佳為1℃/分鐘以下。當然,並不局限於575℃以上的設定溫度,例如當最高到達溫度為540℃時,亦可以在540℃至510℃的溫度上至少通過20分鐘以上,較佳為在(T-500)×t的值成為800以上之條件下通過。若將最高到達溫度在550℃以上提高到略高的溫度,則能夠確保生產性,並能夠得到期望的金相組織。 As another heat treatment method, in the case of a continuous heat treatment furnace in which a hot-extruded material, a hot-forged product, or a material for cold-drawing or a wire is moved in a heat source, if it exceeds 620 ° C, the problem is as described above. However, by temporarily raising the temperature of the material to 575 ° C or higher and 620 ° C or lower, and then maintaining the temperature in a temperature range of 510 ° C or higher and 575 ° C or lower for 20 minutes or more, that is, 510 ° C or higher and The metallographic structure can be improved by cooling at a temperature range of 575 ° C or lower at an average cooling rate of 0.1 ° C / minute or more and 2.5 ° C / minute or less. The average cooling rate in the temperature range of 575 ° C to 510 ° C is preferably 2 ° C / min or less, and more preferably 1.5 ° C / min. Minutes or less, more preferably 1 ° C / minute or less. Of course, it is not limited to a set temperature of 575 ° C or higher. For example, when the maximum temperature reached is 540 ° C, it can also pass at a temperature of 540 ° C to 510 ° C for at least 20 minutes, preferably (T-500) × The value of t is passed under conditions of 800 or more. Increasing the maximum reaching temperature to 550 ° C. or higher to a slightly higher temperature can ensure productivity and obtain a desired metallographic structure.
熱處理的優點並非僅提高耐蝕性、高溫特性。若針對熱加工材料,以3%~20%的加工率實施冷加工(例如冷拉伸或拉線),繼而進行510℃以上且575℃以下的熱處理,或者在與其相當之連續退火爐中進行熱處理,則抗拉強度成為550N/mm2以上,超過熱加工材料的抗拉強度。同時,熱處理材料的衝擊特性超過熱加工材料的衝擊特性。具體而言,熱處理材料的衝擊特性有時至少達到14J/cm2以上、17J/cm2以上或20J/cm2以上。而且,強度指數超過690。 認為該原理如下。當冷加工率為3~20%、加熱溫度為510℃~575℃時,α相、κ相這兩種相雖然充分得到恢復,但兩種相中多少殘留有加工應變。在金相組織中,硬質的γ相減少時,κ相增加,針狀κ相存在於α相內,α相增強。其結果,延展性、衝擊特性、抗拉強度、高溫特性、強度指數均超過熱加工材料。作為易削性銅合金,在廣泛地一般使用之銅合金中,若在實施了3~20%的冷加工之後加熱至 510℃~575℃,則藉由再結晶而變軟。 The advantage of heat treatment is not only to improve corrosion resistance and high temperature characteristics. For hot-worked materials, cold working (such as cold drawing or wire drawing) is performed at a processing rate of 3% to 20%, followed by heat treatment at 510 ° C to 575 ° C, or heat treatment in a continuous annealing furnace equivalent thereto , The tensile strength becomes 550 N / mm 2 or more, which exceeds that of the hot-worked material. At the same time, the impact characteristics of heat-treated materials exceed the impact characteristics of hot-worked materials. Specifically, the impact property is sometimes heat-treated material of at least 14J / cm 2 or more, 17J / cm 2 or more 20J / cm 2 or more. Moreover, the intensity index exceeds 690. The principle is considered as follows. When the cold working rate is 3 to 20% and the heating temperature is 510 ° C to 575 ° C, although the two phases, α phase and κ phase, are fully recovered, processing strain remains in the two phases to some extent. In the metallurgical structure, when the hard γ phase decreases, the κ phase increases, the needle-shaped κ phase exists in the α phase, and the α phase increases. As a result, the ductility, impact characteristics, tensile strength, high temperature characteristics, and strength index all exceeded that of hot-worked materials. As a free-cutting copper alloy, among widely used copper alloys, if it is heated to 510 ° C to 575 ° C after cold working at 3 to 20%, it is softened by recrystallization.
當然,若在規定的熱處理之後以15%以下的冷加工率實施冷加工,則衝擊特性變得略低,但製成強度更高的材料,強度指數超過690。 Of course, if cold working is performed at a cold working rate of 15% or less after a predetermined heat treatment, the impact characteristics become slightly lower, but a material with a higher strength is obtained, and the strength index exceeds 690.
藉由採用該種製造製程,製成耐蝕性優異,且衝擊特性、延展性、強度、切削性優異之合金。 By adopting this manufacturing process, an alloy having excellent corrosion resistance and excellent impact characteristics, ductility, strength, and machinability is produced.
在該等熱處理中,材料亦冷卻至常溫,但在冷卻過程中,需要將在470℃至380℃的溫度區域的平均冷卻速度設為超過2.5℃/分鐘且小於500℃/分鐘。在470℃至380℃的溫度區域的平均冷卻速度,較佳為4℃/分鐘以上。亦即,需要以500℃附近為界而加快平均冷卻速度。通常,從爐中進行的冷卻中,溫度更低的一方的平均冷卻速度越慢。 In these heat treatments, the material is also cooled to normal temperature, but in the cooling process, it is necessary to set the average cooling rate in a temperature range of 470 ° C to 380 ° C to exceed 2.5 ° C / minute and less than 500 ° C / minute. The average cooling rate in a temperature range of 470 ° C to 380 ° C is preferably 4 ° C / min or more. That is, it is necessary to increase the average cooling rate with a boundary around 500 ° C. Generally, the lower the temperature of the cooling performed from the furnace, the slower the average cooling rate.
關於本實施形態的合金的金相組織,在製造製程中重要的是,在熱處理後或熱加工後的冷卻過程中,在470℃至380℃的溫度區域的平均冷卻速度。當平均冷卻速度為2.5℃/分鐘以下時,μ相所佔之比例增大。μ相主要以晶粒邊界、相邊界為中心而形成。在惡劣環境下,μ相比α相、κ相的耐蝕性差,因此成為μ相的選擇腐蝕和晶界腐蝕的原因。又,與γ相相同地,μ相成為應力集中源或成為晶界滑移的原因,降低衝擊特性和高溫強度。較佳為在熱加工後的冷卻中,在470℃至380℃的溫度區域的平均冷 卻速度超過2.5℃/分鐘,較佳為4℃/分鐘以上,更佳為8℃/分鐘以上,進一步較佳為12℃/分鐘以上。在熱加工後材料溫度從580℃以上的高溫急冷時,例如,若以500℃/分鐘以上的平均冷卻速度進行冷卻,則可能導致殘留有許多β相、γ相。因此,平均冷卻速度的上限較佳為小於500℃/分鐘,更佳為300℃/分鐘以下。 Regarding the metallurgical structure of the alloy of this embodiment, it is important in the manufacturing process that the average cooling rate in the temperature range of 470 ° C to 380 ° C during the cooling process after heat treatment or after hot working. When the average cooling rate is 2.5 ° C / min or less, the proportion of the μ phase increases. The μ phase is formed mainly around the grain boundaries and phase boundaries. In the harsh environment, μ is inferior to α-phase and κ-phase in corrosion resistance, and therefore causes the selective corrosion and grain boundary corrosion of the μ-phase. In addition, like the γ phase, the μ phase becomes a stress concentration source or a cause of grain boundary slip, and reduces impact characteristics and high-temperature strength. Preferably, in the cooling after hot working, the average cooling in the temperature range of 470 ° C to 380 ° C However, the speed exceeds 2.5 ° C / min, preferably 4 ° C / min or more, more preferably 8 ° C / min or more, and even more preferably 12 ° C / min or more. When the material temperature is quenched from a high temperature of 580 ° C or higher after hot working, for example, if it is cooled at an average cooling rate of 500 ° C / minute or more, many β phases and γ phases may remain. Therefore, the upper limit of the average cooling rate is preferably less than 500 ° C / minute, and more preferably 300 ° C / minute or less.
若用2000倍或5000倍的電子顯微鏡觀察金相組織,則是否存在μ相之邊界的平均冷卻速度在470℃至380℃的溫度區域中約為8℃/分鐘。尤其,較大影響各種特性之臨界的平均冷卻速度在470℃至380℃的溫度區域中為2.5℃/分鐘或4℃/分鐘。當然,μ相的出現亦依賴於組成,Cu濃度越高、Si濃度越高、金相組織的關係式f1的值越大、f2的值越低,μ相的形成越快速進行。 When the metallographic structure is observed with an electron microscope at a magnification of 2000 or 5000, the average cooling rate of the presence or absence of a μ phase boundary is about 8 ° C./min in a temperature range of 470 ° C. to 380 ° C. In particular, the critical average cooling rate that greatly affects various characteristics is 2.5 ° C./minute or 4 ° C./minute in a temperature range of 470 ° C. to 380 ° C. Of course, the appearance of the μ phase also depends on the composition. The higher the Cu concentration, the higher the Si concentration, the larger the value of the relationship f1 of the metallographic structure, and the lower the value of f2, the faster the formation of the μ phase.
亦即,若在470℃至380℃的溫度區域的平均冷卻速度慢於8℃/分鐘,則析出於晶界之μ相的長邊的長度約超過1μm,隨著平均冷卻速度變慢而進一步生長。而且,若平均冷卻速度約成為5℃/分鐘,則μ相的長邊的長度從約3μm成為約10μm。若平均冷卻速度約成為2.5℃/分鐘以下,則μ相的長邊的長度超過15μm,在某些情況下超過25μm。 若μ相的長邊的長度約達到10μm,則在1000倍的金屬顯微鏡中能夠區分μ相與晶粒邊界,從而能夠進行觀察。另 一方面,平均冷卻速度的上限雖然依熱加工溫度等而不同,但若平均冷卻速度過快,則高溫下形成之構成相直接維持至常溫,κ相增加,影響耐蝕性、衝擊特性之β相、γ相增加。因此,主要來自580℃以上的溫度區域的平均冷卻速度係重要,以小於500℃/分鐘的平均冷卻速度進行冷卻為較佳,更佳為300℃/分鐘以下。 That is, if the average cooling rate in the temperature range of 470 ° C to 380 ° C is slower than 8 ° C / min, the length of the long side of the μ phase precipitated at the grain boundary exceeds about 1 μm, and further progresses as the average cooling rate becomes slower. Grow. When the average cooling rate is about 5 ° C./minute, the length of the long side of the μ phase is changed from about 3 μm to about 10 μm. When the average cooling rate is about 2.5 ° C./min or less, the length of the long side of the μ phase exceeds 15 μm, and in some cases exceeds 25 μm. When the length of the long side of the μ-phase reaches about 10 μm, the μ-phase and the grain boundary can be distinguished in a 1000-fold metal microscope, and observation can be performed. another On the one hand, although the upper limit of the average cooling rate varies depending on the hot working temperature, etc., if the average cooling rate is too fast, the constituent phases formed at high temperatures are directly maintained to normal temperature, and the κ phase increases, which affects the β phase of corrosion resistance and impact characteristics. And γ phase increase. Therefore, the average cooling rate mainly from a temperature range of 580 ° C or higher is important, and it is preferable to perform cooling at an average cooling rate of less than 500 ° C / minute, and more preferably 300 ° C / minute or less.
目前,含有Pb之黃銅合金佔銅合金的擠出材料的絕大部分。在該含有Pb之黃銅合金的情況下,如專利文獻1所述,以350~550℃的溫度依需要而進行熱處理。下限之350℃係進行再結晶且材料大致軟化之溫度。上限之550℃中,再結晶結束。又,由於提高溫度而存在能量上的問題,又,若以超過550℃的溫度進行熱處理,則β相明顯增加。因此,考慮上限為550℃。作為一般的製造設備,使用分次式熔爐或連續爐,並以規定的溫度保持1~8小時。 在分次式熔爐的情況下,進行爐冷,或在爐冷後約從300℃起進行氣冷。在連續爐的情況下,在材料溫度降低至約300℃之前,以比較慢的速度進行冷卻。具體而言,除了所保持之規定的溫度以外,在470℃至380℃的溫度區域以約0.5~約4℃/分鐘的平均冷卻速度進行冷卻。以與本實施形態的合金的製造方法不同之冷卻速度進行冷卻。 Currently, brass alloys containing Pb account for most of the extrusion materials of copper alloys. In the case of the brass alloy containing Pb, as described in Patent Document 1, heat treatment is performed at a temperature of 350 to 550 ° C as needed. The lower limit of 350 ° C is the temperature at which recrystallization occurs and the material is approximately softened. At an upper limit of 550 ° C, recrystallization is completed. In addition, there is an energy problem due to an increase in temperature. When the heat treatment is performed at a temperature exceeding 550 ° C, the β phase increases significantly. Therefore, the upper limit is considered to be 550 ° C. As a general manufacturing facility, a split furnace or continuous furnace is used, and it is maintained at a predetermined temperature for 1 to 8 hours. In the case of a split-type furnace, furnace cooling is performed, or after the furnace cooling, air cooling is performed from about 300 ° C. In the case of a continuous furnace, the material is cooled at a relatively slow rate before the temperature of the material is reduced to about 300 ° C. Specifically, in addition to the predetermined temperature maintained, cooling is performed at an average cooling rate of about 0.5 to about 4 ° C / min in a temperature range of 470 ° C to 380 ° C. The cooling is performed at a cooling rate different from that of the method for producing the alloy of this embodiment.
(低溫退火) (Low temperature annealing)
在棒材、鍛造品中,為了去除殘餘應力和矯正棒材,有時會在再結晶溫度以下的溫度對棒材、鍛造品進行低溫退火。作為該低溫退火的條件,將材料溫度設為240℃以上且350℃以下,將加熱時間設為10分鐘至300分鐘為較佳。進而當將低溫退火的溫度(材料溫度)設為T(℃)、將加熱時間設為t(分鐘)時,在滿足150(T-220)×(t)1/2 1200的關係之條件下實施低溫退火為較佳。再者,此處設為從比達到規定的溫度T(℃)之溫度低10℃之溫度(T-10)開始,對加熱時間t(分鐘)進行計數(測量)者。 In the case of bars and forged products, in order to remove residual stresses and correct the bars, the bars and forged products may be annealed at a temperature lower than the recrystallization temperature. As conditions for this low-temperature annealing, the material temperature is preferably 240 ° C. or higher and 350 ° C. or lower, and the heating time is preferably 10 minutes to 300 minutes. Furthermore, when the temperature (material temperature) of the low-temperature annealing is set to T (° C) and the heating time is set to t (minutes), the temperature is 150. (T-220) × (t) 1/2 It is preferable to perform low temperature annealing under the conditions of 1200. Here, it is assumed that the heating time t (minutes) is counted (measured) starting from a temperature (T-10) which is 10 ° C lower than the temperature reaching the predetermined temperature T (° C).
當低溫退火的溫度低於240℃時,殘餘應力的去除不夠充分,並且不會充分進行矯正。當低溫退火的溫度超過350℃時,以晶粒邊界、相邊界為中心形成μ相。若低溫退火的時間小於10分鐘,則殘餘應力的去除不夠充分。 若低溫退火的時間超過300分鐘則μ相增大。隨著提高低溫退火的溫度或增加時間,μ相增大,從而耐蝕性、衝擊特性及高溫強度降低。然而,藉由實施低溫退火無法避免μ相的析出,如何去除殘餘應力並且將μ相的析出限制在最小限度成為關鍵。 When the temperature of the low temperature annealing is lower than 240 ° C, the residual stress is not sufficiently removed, and correction is not performed sufficiently. When the temperature of the low-temperature annealing exceeds 350 ° C., a μ phase is formed around the grain boundary and the phase boundary. If the low-temperature annealing time is less than 10 minutes, the residual stress is not sufficiently removed. When the low-temperature annealing time exceeds 300 minutes, the μ phase increases. As the temperature or time of the low-temperature annealing is increased, the μ phase increases, so that the corrosion resistance, impact characteristics, and high-temperature strength decrease. However, the precipitation of the μ-phase cannot be avoided by performing low-temperature annealing, and how to remove the residual stress and limit the precipitation of the μ-phase to the minimum becomes the key.
再者,(T-220)×(t)1/2的值的下限為150,較佳為180以上,更佳為200以上。又,(T-220)×(t)1/2的值的上限為1200,較佳為1100以下,更佳為1000以下。 The lower limit of the value of (T-220) × (t) 1/2 is 150, preferably 180 or more, and more preferably 200 or more. The upper limit of the value of (T-220) × (t) 1/2 is 1200, preferably 1100 or less, and more preferably 1000 or less.
藉由該種製造方法來製造本發明的第1、2實施形態之易削性銅合金。 According to this manufacturing method, the free-cutting copper alloys according to the first and second embodiments of the present invention are manufactured.
熱加工製程、熱處理(退火)製程、低溫退火製程為對銅合金進行加熱之製程。當不進行低溫退火製程時,或者在低溫退火製程之後進行熱加工製程或熱處理(退火)製程時(當低溫退火製程未成為在最後對銅合金進行加熱之製程時),與冷加工的有無無關地,熱加工製程、熱處理(退火)製程中之後進行之製程成為重要者。當在熱處理(退火)製程之後進行熱加工製程或在熱加工製程之後不進行熱處理(退火)製程時(當當熱加工製程成為在最後對銅合金進行加熱之製程時),熱加工製程需要滿足上述加熱條件和冷卻條件。當在熱加工製程之後進行熱處理(退火)製程或在熱處理(退火)製程之後不進行熱加工製程時(當熱處理(退火)製程成為在最後對銅合金進行加熱之製程時),熱處理(退火)製程需要滿足上述加熱條件和冷卻條件。例如,當在熱鍛造製程之後不進行熱處理(退火)製程時,熱鍛造製程需要滿足上述熱鍛造的加熱條件和冷卻條件。當在熱鍛造製程之後進行熱處理(退火)製程時,熱處理(退火)製程需要滿足上述熱處理(退火)的加熱條件和冷卻條件。該情況下,熱鍛造製程未必一定要滿足上述熱鍛造的加熱條件和冷卻條件。 The hot working process, the heat treatment (annealing) process, and the low temperature annealing process are processes for heating a copper alloy. When the low temperature annealing process is not performed, or the hot working process or the heat treatment (annealing) process is performed after the low temperature annealing process (when the low temperature annealing process does not become the process of heating the copper alloy last), regardless of the presence or absence of cold working The processes performed after the hot working process and the heat treatment (annealing) process become important. When the hot working process is performed after the heat treatment (annealing) process or the heat treatment (annealing) process is not performed after the hot working process (when the hot working process becomes the process of heating the copper alloy last), the hot working process needs to meet the above Heating and cooling conditions. Heat treatment (annealing) when a heat treatment (annealing) process is performed after the hot working process or no heat processing process is performed after the heat treatment (annealing) process (when the heat treatment (annealing) process becomes the process of heating the copper alloy last) The manufacturing process needs to meet the above heating conditions and cooling conditions. For example, when the heat treatment (annealing) process is not performed after the hot forging process, the hot forging process needs to satisfy the heating conditions and cooling conditions of the hot forging described above. When the heat treatment (annealing) process is performed after the hot forging process, the heat treatment (annealing) process needs to satisfy the heating conditions and cooling conditions of the above heat treatment (annealing). In this case, the hot forging process does not necessarily have to satisfy the heating conditions and cooling conditions of the hot forging described above.
在低溫退火製程中,材料溫度為240℃以上且350℃以下,該溫度與是否生成μ相有關,與γ相減少之溫度範圍(575~510℃)無關。這樣,低溫退火製程中的材料溫度與γ相的增減無關。因此,當在熱加工製程或熱處理(退火)製程之後進行低溫退火製程時(當低溫退火製程成為在最後對銅合金進行加熱之製程時),與低溫退火製程的條件一同,低溫退火製程之前的製程(在立即進行低溫退火製程之前對銅合金進行加熱之製程)的加熱條件和冷卻條件變得重要,低溫退火製程和低溫退火製程之前的製程需要滿足上述加熱條件和冷卻條件。詳細而言,在低溫退火製程之前的製程中,在熱加工製程、熱處理(退火)製程中、在該製程之後進行之製程的加熱條件和冷卻條件亦變得重要,需要滿足上述加熱條件和冷卻條件。當在低溫退火製程之後進行熱加工製程或熱處理(退火)製程時,如前述那樣在熱加工製程、熱處理(退火)製程中、該製程之後進行之製程變得重要,需要滿足上述加熱條件和冷卻條件。再者,亦可以在低溫退火製程之前或之後進行熱加工製程或熱處理(退火)製程。 In the low temperature annealing process, the material temperature is above 240 ° C and below 350 ° C. This temperature is related to whether or not the μ phase is formed, and has nothing to do with the temperature range (575 ~ 510 ° C) where the γ phase is reduced. In this way, the material temperature in the low temperature annealing process has nothing to do with the increase or decrease of the γ phase. Therefore, when the low temperature annealing process is performed after the hot working process or the heat treatment (annealing) process (when the low temperature annealing process becomes the process of heating the copper alloy last), together with the conditions of the low temperature annealing process, the temperature before the low temperature annealing process The heating conditions and cooling conditions of the manufacturing process (the process of heating the copper alloy immediately before the low temperature annealing process) become important. The low temperature annealing process and the processes before the low temperature annealing process need to meet the above heating conditions and cooling conditions. In detail, in the process before the low temperature annealing process, the heating conditions and cooling conditions in the hot working process, the heat treatment (annealing) process, and the process performed after the process also become important, and it is necessary to satisfy the above heating conditions and cooling condition. When a hot working process or a heat treatment (annealing) process is performed after the low temperature annealing process, as described above, in the hot working process, the heat treatment (annealing) process, and the process performed after the process becomes important, it is necessary to meet the above heating conditions and cooling condition. Furthermore, a hot working process or a heat treatment (annealing) process may be performed before or after the low temperature annealing process.
依設為如上構成之本發明的第1、第2實施形態之易削性合金,如上述那樣規定了合金組成、組成關係式、金相組織、組織關係式,因此在惡劣環境下的耐蝕性、衝 擊特性及高溫強度優異。又,即使Pb的含量少,亦能夠得到優異之切削性。 The free-cutting alloy according to the first and second embodiments of the present invention configured as described above has the alloy composition, the composition relational expression, the metallographic structure, and the structural relational expression defined as described above, so the corrosion resistance under harsh environments Chong Excellent impact properties and high temperature strength. Moreover, even if the content of Pb is small, excellent machinability can be obtained.
以上,對本發明的實施形態進行了說明,但本發明並不限定於此,在不脫離其發明的技術要求之範圍內可適當進行變更。 As mentioned above, although embodiment of this invention was described, this invention is not limited to this, It can change suitably in the range which does not deviate from the technical requirement of the invention.
【實施例】 [Example]
以下示出為了確認本發明的效果而進行之確認實驗的結果。再者,以下的實施例係用於說明本發明的效果者,實施例中所記載之構成要件、製程、條件並非限定本發明的技術範圍者。 The results of confirmation experiments performed to confirm the effects of the present invention are shown below. In addition, the following examples are for explaining the effect of the present invention, and the constituent elements, processes, and conditions described in the examples do not limit the technical scope of the present invention.
(實施例1) (Example 1)
<實際操作實驗> <Practical experiments>
利用在實際操作中使用之低頻熔爐及半連續鑄造機實施了銅合金的原型試驗。表2中示出合金組成。再者,由於使用了實際操作設備,因此在表2所示之合金中亦對雜質進行了測定。又,製造製程設為表5~表10所示之條件。 A prototype test of copper alloy was carried out using a low-frequency furnace and a semi-continuous casting machine used in actual operation. Table 2 shows the alloy composition. In addition, since actual operating equipment was used, impurities were also measured in the alloys shown in Table 2. The manufacturing process was performed under the conditions shown in Tables 5 to 10.
(製程No.A1~A12、AH1~AH9) (Process No.A1 ~ A12, AH1 ~ AH9)
利用實際操作之低頻熔爐及半連續鑄造機製造了直徑240mm的小坯。原料使用了依照實際操作者。將小坯切斷成800mm的長度並進行了加熱。進行熱擠壓而設為直徑25.6mm的圓棒狀並捲繞成線圈(擠出材料)。繼而,藉由 線圈的保溫和風扇的調整,在575℃~510℃的溫度區域及470℃至380℃的溫度區域,以20℃/分鐘的平均冷卻速度對擠出材料進行冷卻。在380℃以下的溫度區域中亦以約20℃/分鐘的平均冷卻速度進行冷卻。以熱擠壓的最後階段為中心並使用輻射溫度計來進行溫度測定,測定了從利用擠壓機擠出時起約3秒後的擠出材料的溫度。再者,使用了Daido Steel Co.,Ltd.製造的DS-06DF型輻射溫度計。 A small billet with a diameter of 240 mm was manufactured using a low-frequency furnace and a semi-continuous casting machine in actual operation. The raw materials are used according to the actual operator. The billet was cut to a length of 800 mm and heated. It was hot-extruded to have a round rod shape with a diameter of 25.6 mm, and was wound into a coil (extruded material). Then, by The insulation of the coil and the adjustment of the fan, in the temperature range of 575 ° C to 510 ° C and the temperature range of 470 ° C to 380 ° C, cool the extruded material at an average cooling rate of 20 ° C / min. Cooling is also performed in a temperature range of 380 ° C or lower at an average cooling rate of about 20 ° C / minute. The temperature was measured using a radiation thermometer around the last stage of hot extrusion, and the temperature of the extruded material was measured about 3 seconds after the extruder was extruded. In addition, a DS-06DF radiation thermometer manufactured by Daido Steel Co., Ltd. was used.
確認到該擠出材料的溫度的平均值為表5所示之溫度的±5℃(在(表5所示之溫度)-5℃~(表5所示之溫度)+5℃的範圍內)。 It was confirmed that the average value of the temperature of the extruded material was ± 5 ° C of the temperature shown in Table 5 (within the temperature shown in Table 5) -5 ° C to (temperature shown in Table 5) + 5 ° C. ).
在製程No.AH2、A9、AH9中,分別將擠壓溫度設為760℃、680℃、580℃。在除了製程No.AH2、A9、AH9以外的製程中,將擠壓溫度設為640℃。在擠壓溫度為580℃的製程No.AH9中,所準備之3種材料均未能擠出至最後而被放棄。 In process Nos. AH2, A9, and AH9, the extrusion temperatures were set to 760 ° C, 680 ° C, and 580 ° C, respectively. In processes other than Process Nos. AH2, A9, and AH9, the extrusion temperature was set to 640 ° C. In process No. AH9 with an extrusion temperature of 580 ° C, the three materials prepared were not extruded to the end and were abandoned.
擠出後,在製程No.AH1、AH2中僅實施了矯正。 After extrusion, only correction was performed in process Nos. AH1 and AH2.
在製程No.A10、A11中,對直徑25.6mm的擠出材料進行了熱處理。繼而,在製程No.A10、A11中,實施冷加工率分別為約5%、約9%的冷拉伸,然後進行矯正,使直徑分別成為25mm、24.4mm(在熱處理後進行複合拉伸、矯正)。 In process Nos. A10 and A11, the extruded material having a diameter of 25.6 mm was heat-treated. Next, in process Nos. A10 and A11, cold drawing was performed at a cold working ratio of about 5% and about 9%, respectively, and then corrected to make the diameters 25mm and 24.4mm (composite stretching and correction after heat treatment were performed). ).
在製程No.A12中,實施冷加工率約為9%的冷拉伸,然後進行矯正,使直徑成為24.4mm(複合拉伸、矯正)。 繼而進行了熱處理。 In process No. A12, cold drawing was performed with a cold working ratio of about 9%, and then correction was performed so that the diameter became 24.4 mm (composite drawing, correction). This was followed by heat treatment.
在除上述以外的製程中,實施冷加工率約為5%的冷拉伸,然後進行矯正,使直徑成為25mm(複合拉伸、矯正)。 繼而進行了熱處理。 In processes other than the above, cold drawing with a cold working ratio of about 5% is performed, and then correction is performed so that the diameter becomes 25 mm (composite drawing, correction). This was followed by heat treatment.
如表5所示,關於熱處理條件,改變了熱處理的溫度至500℃至635℃,亦改變了保持時間至5分鐘至180分鐘。 As shown in Table 5, regarding the heat treatment conditions, the temperature of the heat treatment was changed to 500 ° C to 635 ° C, and the holding time was also changed to 5 minutes to 180 minutes.
在製程No.A1~A6、A9~A12、AH3、AH4、AH6中,使用分次式熔爐,改變了冷卻過程的在575℃至510℃的溫度區域的平均冷卻速度或在470℃至380℃的溫度區域的平均冷卻速度。 In process Nos. A1 to A6, A9 to A12, AH3, AH4, and AH6, a split furnace is used to change the average cooling rate in the temperature range of 575 ° C to 510 ° C or 470 ° C to 380 ° C in the cooling process. The average cooling rate in the temperature region.
在製程No.A7、A8、AH5、AH7、AH8中,使用連續退火爐,在高溫下進行短時間的加熱,繼而,改變了在575℃至510℃的溫度區域的平均冷卻速度或在470℃至380℃的溫度區域的平均冷卻速度。 In process Nos. A7, A8, AH5, AH7, and AH8, a continuous annealing furnace is used to heat at a high temperature for a short time, and then the average cooling rate in the temperature range of 575 ° C to 510 ° C or 470 ° C is changed. The average cooling rate in the temperature range to 380 ° C.
再者,在下表中,用“○”表示在熱處理前進行了複合拉伸、矯正的情況,用“-”表示未進行的情況。 In the table below, "○" indicates that the composite stretching and correction were performed before the heat treatment, and "-" indicates that it was not performed.
(製程No.B1~B3、BH1~BH3) (Process No.B1 ~ B3, BH1 ~ BH3)
將在製程No.A10中得到之直徑25mm的材料(棒材)切斷為3m的長度。繼而,在模板上排列該棒材,以矯正 目的進行了低溫退火。將此時的低溫退火條件作為表7所示之條件。 The material (rod) with a diameter of 25 mm obtained in Process No. A10 was cut to a length of 3 m. The bars are then arranged on a template to correct Aim Low temperature annealing was performed. The low-temperature annealing conditions at this time were used as the conditions shown in Table 7.
再者,表中的條件式的值為下述式的值。 The value of the conditional expression in the table is the value of the following expression.
(條件式)=(T-220)×(t)1/2 (Conditional expression) = (T-220) × (t) 1/2
T:溫度(材料溫度)(℃)、t:加熱時間(分鐘) T: temperature (material temperature) (° C), t: heating time (minutes)
結果,只有製程No.BH1的線性度差。 As a result, only the linearity of the process No. BH1 was poor.
(製程No.C0、C1、C2、CH1、CH2) (Process No.C0, C1, C2, CH1, CH2)
利用實際操作之低頻熔爐及半連續鑄造機製造了直徑240mm的鑄錠(小坯)。原料使用了依照實際操作者。將小坯切斷成500mm的長度並進行了加熱。而且,進行熱擠壓而設為直徑50mm的圓棒狀擠出材料。該擠出材料以直棒形狀在擠出台被擠出。以擠壓的最後階段為中心並使用輻射溫度計來進行溫度測定,測定了從利用擠壓機擠出之時點起約3秒後的擠出材料的溫度。確認到該擠出材料的溫度的平均值為表8所示之溫度的±5℃(在(表8所示之溫度)-5℃~(表8所示之溫度)+5℃的範圍內)。再者,擠壓後的575℃至510℃的平均冷卻速度及470℃至380℃的平均冷卻速度為15℃/分鐘(擠出材料)。在後述製程中,將在製程No.C0、CH2中獲得之擠出材料(圓棒)用作了鍛造用原材料。在製程No.C1、C2、CH1中,於560℃加熱60分鐘,繼而改變了470℃至380℃的平均冷卻速度。 An ingot (small billet) with a diameter of 240 mm was manufactured by using a low-frequency furnace and a semi-continuous casting machine in actual operation. The raw materials are used according to the actual operator. The billet was cut to a length of 500 mm and heated. Then, a hot extruded material was used as a round rod-shaped extruded material having a diameter of 50 mm. The extruded material was extruded in a straight bar shape at an extrusion station. The temperature was measured using a radiation thermometer around the last stage of the extrusion, and the temperature of the extruded material was measured about 3 seconds after the point of extrusion with the extruder. It was confirmed that the average value of the temperature of the extruded material was within ± 5 ° C of the temperature shown in Table 8 (within the temperature shown in Table 8) -5 ° C to (temperature shown in Table 8) + 5 ° C. ). In addition, the average cooling rate of 575 ° C to 510 ° C and the average cooling rate of 470 ° C to 380 ° C after extrusion were 15 ° C / minute (extruded material). In the process described later, the extruded material (round bar) obtained in the process Nos. C0 and CH2 was used as a raw material for forging. In process Nos. C1, C2, and CH1, heating was performed at 560 ° C for 60 minutes, and then the average cooling rate of 470 ° C to 380 ° C was changed.
(製程No.D1~D8、DH1~DH5) (Process No.D1 ~ D8, DH1 ~ DH5)
將在製程No.C0中得到之直徑50mm的圓棒切斷為180mm的長度。橫向放置該圓棒,使用熱鍛壓能力150噸的壓機鍛造成厚度成為16mm。在剛熱鍛造成規定的厚度之後約經過3秒後,使用輻射溫度計進行了溫度的測定。確認到熱鍛溫度(熱加工溫度)為表9所示之溫度±5℃的範圍(在(表9所示之溫度)-5℃~(表9所示之溫度)+5℃的範圍內)。 A round rod having a diameter of 50 mm obtained in Process No. C0 was cut to a length of 180 mm. The round bar was placed in the horizontal direction, and the thickness was 16 mm by using a hot forging press with a capacity of 150 tons. The temperature was measured using a radiation thermometer after about 3 seconds after the hot forging was performed to a predetermined thickness. It was confirmed that the hot forging temperature (hot working temperature) was within the range of the temperature ± 5 ° C shown in Table 9 (within the temperature shown in Table 9) -5 ° C ~ (the temperature shown in Table 9) + 5 ° C ).
在製程No.D6、DH5中,在熱鍛造後改變在575℃至510℃的溫度區域的平均冷卻速度來實施。在製程No.D6、DH5以外的製程中,在熱鍛造後以20℃/分鐘的平均冷卻速度進行冷卻。 In process Nos. D6 and DH5, the average cooling rate in a temperature range of 575 ° C to 510 ° C was changed after hot forging and implemented. In processes other than Process No. D6 and DH5, cooling is performed at an average cooling rate of 20 ° C./minute after hot forging.
在製程No.DH1、D6、DH5中,藉由熱鍛造後的冷卻而結束了試樣的製作操作。在製程No.DH1、D6、DH5以外的製程中,在熱鍛造後進行了以下熱處理。 In process Nos. DH1, D6, and DH5, the sample preparation operation was completed by cooling after hot forging. In processes other than Process Nos. DH1, D6, and DH5, the following heat treatment was performed after hot forging.
在製程No.D1~D4、DH2中,用分次式熔爐進行熱處理,並改變熱處理的溫度、在575℃至510℃的溫度區域的平均冷卻速度及在470℃至380℃的溫度區域的平均冷卻速度來實施。在製程No.D5、DH3、DH4中,用連續爐以600℃加熱3分鐘或2分鐘,並改變平均冷卻速度來實施。 In process Nos. D1 to D4 and DH2, heat treatment is performed in a split furnace, and the temperature of the heat treatment is changed, the average cooling rate in a temperature range of 575 ° C to 510 ° C, and the average value in a temperature range of 470 ° C to 380 ° C. The cooling rate is implemented. In the process No. D5, DH3, and DH4, the heating was performed at 600 ° C for 3 minutes or 2 minutes in a continuous furnace, and the average cooling rate was changed.
再者,熱處理的溫度為材料的最高到達溫度,作為保 持時間,採用了在最高到達溫度至(最高到達溫度-10℃)的溫度區域中保持之時間。 In addition, the temperature of heat treatment is the highest reaching temperature of the material. The holding time is a holding time in a temperature range from the highest reaching temperature to (the highest reaching temperature -10 ° C).
<實驗室實驗> <Laboratory experiment>
使用實驗室設備實施了銅合金的原型試驗。表3及表4中示出合金組成。再者,剩餘部分為Zn及不可避免的雜質。表2所示之組成的銅合金亦用於實驗室實驗中。又,製造製程設為表11及表12所示之條件。 A prototype test of a copper alloy was performed using laboratory equipment. Tables 3 and 4 show alloy compositions. Moreover, the remainder is Zn and unavoidable impurities. The copper alloys of the composition shown in Table 2 were also used in laboratory experiments. The manufacturing process was performed under the conditions shown in Tables 11 and 12.
(製程No.E1~E3、EH1) (Process No.E1 ~ E3, EH1)
在實驗室中,以規定的成分比熔解了原料。將熔液澆鑄於直徑100mm、長度180mm的金屬模中,從而製作了小坯。對該小坯進行加熱,在製程No.E1、EH1中擠出為直徑25mm的圓棒並進行矯正。在製程No.E2、E3中擠出為直徑40mm的圓棒並進行矯正。表11中,用“○”表示進行了矯正之情況。 In the laboratory, the raw materials were melted at a prescribed composition ratio. The molten metal was cast into a metal mold having a diameter of 100 mm and a length of 180 mm to prepare a small billet. This small billet was heated and extruded into a round bar with a diameter of 25 mm in process Nos. E1 and EH1 and corrected. In process Nos. E2 and E3, a round rod with a diameter of 40 mm was extruded and corrected. In Table 11, "○" indicates that the correction was performed.
在擠壓試驗機剛停止後使用輻射溫度計進行了溫度測定。結果相當於從利用擠壓機擠出時起約3秒後的擠出材料的溫度。 The temperature was measured using a radiation thermometer immediately after the extrusion tester was stopped. The result corresponds to the temperature of the extruded material after about 3 seconds from the time of extrusion with an extruder.
在製程No.EH1、E2中,以擠壓作為試樣的製作操作結束。在製程No.E2中得到之擠出材料在後述製程中被用作熱鍛造原材料。 In the process Nos. EH1 and E2, the production operation using extrusion as a sample is completed. The extruded material obtained in the process No. E2 is used as a raw material for hot forging in a process described later.
又,藉由連續鑄造製作出直徑40mm的連續鑄造棒, 在後述製程中被用作熱鍛造原材料。 In addition, a continuous casting rod with a diameter of 40 mm was produced by continuous casting. It is used as a hot forging material in a process described later.
在製程No.E1、E3中,在擠壓後以表11所示之條件進行了熱處理(退火)。 In process Nos. E1 and E3, heat treatment (annealing) was performed under the conditions shown in Table 11 after extrusion.
(製程No.F1~F5、FH1、FH2) (Process No.F1 ~ F5, FH1, FH2)
將在製程No.E2中得到之直徑40mm的圓棒切斷成180mm的長度。橫向放置製程No.E2的圓棒或者前述連續鑄造棒,並使用熱鍛壓能力150噸的壓機鍛造成厚度成為15mm。從剛熱鍛造成規定的厚度之後約經過3秒後,使用輻射溫度計進行了溫度的測定。確認到熱鍛溫度(熱加工溫度)為表12所示之溫度±5℃的範圍(在(表12所示之溫度)-5℃~(表12所示之溫度)+5℃的範圍內)。 The round bar having a diameter of 40 mm obtained in Process No. E2 was cut to a length of 180 mm. A round rod of process No. E2 or the aforementioned continuous casting rod was placed in the horizontal direction, and was forged using a hot forging press with a capacity of 150 tons to a thickness of 15 mm. About 3 seconds passed after the hot forging to a predetermined thickness, the temperature was measured using a radiation thermometer. It was confirmed that the hot forging temperature (hot working temperature) was within the range of the temperature ± 5 ° C shown in Table 12 (within the temperature shown in Table 12) -5 ° C to the temperature shown in Table 12 + 5 ° C. ).
將在575℃至510℃的溫度區域的平均冷卻速度及在470℃至380℃的溫度區域的平均冷卻速度分別設為20℃/分鐘、18℃/分鐘。在製程No.FH1中,對在製程No.E2中得到之圓棒實施了熱鍛造,以熱鍛造後的冷卻作為試樣的製作操作結束。 The average cooling rate in a temperature range of 575 ° C to 510 ° C and the average cooling rate in a temperature range of 470 ° C to 380 ° C were set to 20 ° C / minute and 18 ° C / minute, respectively. In the process No. FH1, the round bar obtained in the process No. E2 was subjected to hot forging, and the cooling operation after the hot forging was used as a sample to end.
在製程No.F1、F2、FH2中,對在製程No.E2中得到之圓棒實施了熱鍛造,在熱鍛造後進行了熱處理。改變加熱條件、在575℃至510℃的溫度區域的平均冷卻速度及在470℃至380℃的溫度區域的平均冷卻速度來實施了熱處理(退火)。 In the process Nos. F1, F2, and FH2, the round bar obtained in the process No. E2 was subjected to hot forging, and heat treatment was performed after the hot forging. Heat treatment (annealing) was performed while changing heating conditions, the average cooling rate in a temperature range of 575 ° C to 510 ° C, and the average cooling rate in a temperature range of 470 ° C to 380 ° C.
在製程No.F3、F4中,作為鍛造原材料使用連續鑄造棒進行了熱鍛造。在熱鍛造後改變加熱條件、平均冷卻速度來實施了熱處理(退火)。 In process Nos. F3 and F4, hot forging was performed using a continuous casting rod as a forging material. After hot forging, heat treatment (annealing) was performed by changing heating conditions and average cooling rate.
關於上述試驗材料,藉由以下步驟,對金相組織觀察、耐蝕性(脫鋅腐蝕試驗/浸漬試驗)、切削性進行了評價。 The above test materials were evaluated for metallographic structure observation, corrosion resistance (dezincification corrosion test / immersion test), and machinability by the following procedures.
(金相組織的觀察) (Observation of Metallographic Structure)
藉由以下方法觀察了金相組織,並藉由圖像解析測定了α相、κ相、β相、γ相、μ相的面積率(%)。再者,α’相、β’相、γ’相設為分別包含於α相、β相、γ相中。 The metallographic structure was observed by the following method, and the area ratios (%) of the α phase, κ phase, β phase, γ phase, and μ phase were measured by image analysis. The α 'phase, β' phase, and γ 'phase are included in the α phase, β phase, and γ phase, respectively.
針對各試驗材料的棒材、鍛造品,與長邊方向平行地,或與金相組織的流動方向平行地進行切斷。繼而,對表面進行研磨(鏡面拋光,mirror face polishing),並用過氧化氫與氨水的混合液進行了蝕刻。蝕刻時使用了將3vol%的過氧化氫水3mL與14vol%的氨水22mL進行混合而得之水溶液。於約15℃~約25℃的室溫下,將金屬的研磨面浸漬於該水溶液中約2秒~約5秒。 The bars and forged products of each test material were cut parallel to the longitudinal direction or parallel to the flow direction of the metallographic structure. Then, the surface was polished (mirror face polishing) and etched with a mixed solution of hydrogen peroxide and ammonia. During the etching, an aqueous solution obtained by mixing 3 mL of 3 vol% hydrogen peroxide water and 14 vol% of ammonia water 22 mL was used. At a room temperature of about 15 ° C to about 25 ° C, the polished surface of the metal is immersed in the aqueous solution for about 2 seconds to about 5 seconds.
使用金屬顯微鏡,主要以500倍的倍率觀察了金相組織,並且依金相組織的狀況而以1000倍觀察了金相組織。 在5個視場的顯微照片中,使用圖像處理軟體“PhotoshopCC”手動塗滿了各相(α相、κ相、β相、γ相、μ相)。繼而,藉由圖像處理軟體“WinROOF2013”進行二值化,從而求出了各相的面積率。詳細而言,關於各相,求出5個視場的面積率的平均值,並將平均值設為各相的 相比率。而且,將所有構成相的面積率的總計設為100%。 Using a metal microscope, the metallographic structure was observed mainly at a magnification of 500 times, and the metallographic structure was observed at a magnification of 1,000 times depending on the state of the metallographic structure. In the photomicrographs of 5 fields of view, each phase (α-phase, κ-phase, β-phase, γ-phase, μ-phase) was manually coated with an image processing software "PhotoshopCC". Then, the image processing software "WinROOF2013" was used for binarization to obtain the area ratio of each phase. Specifically, for each phase, an average value of area ratios of 5 fields of view was obtained, and the average value was set as Comparison rate. The total area ratio of all constituent phases is 100%.
藉由以下方法測定了γ相、μ相的長邊的長度。使用500倍或1000倍的金屬顯微照片,在1個視場中測定了γ相的長邊的最大長度。在任意的5個視場中進行該操作,計算所得之γ相的長邊最大長度的平均值,並設為γ相的長邊的長度。同樣地,依據μ相的大小,使用500倍或1000倍的金屬顯微照片,或使用2000倍或5000倍的二次電子像照片(電子顯微照片),在1個視場中測定了μ相的長邊的最大長度。在任意的5個視場中進行該操作,計算所得之μ相的長邊最大長度的平均值,並設為μ相的長邊的長度。 The lengths of the long sides of the γ phase and the μ phase were measured by the following methods. The maximum length of the long side of the γ phase was measured in one field of view using 500 times or 1000 times the metal micrograph. This operation is performed in any of the five fields of view, the average value of the maximum length of the long side of the γ phase is calculated, and the length of the long side of the γ phase is set. Similarly, depending on the size of the μ phase, using 500 or 1000 times metal photomicrographs or 2000 or 5000 times secondary electron image (electron micrograph), μ was measured in one field of view. The maximum length of the long side of the phase. This operation is performed in any of the five fields of view, and the average value of the maximum lengths of the long sides of the μ phase is calculated and set as the length of the long sides of the μ phase.
具體而言,使用打印出約70mm×約90mm尺寸之照片進行了評價。在500倍倍率的情況下,觀察視場的尺寸為276μm×220μm。 Specifically, evaluation was performed using a photo printed with a size of about 70 mm × about 90 mm. In the case of 500x magnification, the size of the observation field of view is 276 μm × 220 μm.
當相的識別困難時,藉由FE-SEM-EBSP(電子背散射繞射圖像(Electron Back Scattering Diffracton Pattern))法,以500倍或2000倍的倍率對相進行了指定。 When phase identification is difficult, the phase is specified at a magnification of 500 or 2000 times by the FE-SEM-EBSP (Electron Back Scattering Diffracton Pattern) method.
又,在改變平均冷卻速度之實施例中,為了確認主要在晶粒邊界析出之μ相的有無,使用JEOL Ltd.製造的JSM-7000F,在加速電壓15kV、電流值(設定值15)的條件下拍攝二次電子像,並以2000倍或5000倍的倍率確認 了金相組織。當能夠用2000倍或5000倍的二次電子像確認μ相,但不能用500倍或1000倍的金屬顯微照片確認μ相時,未計算面積率。亦即,被2000倍或5000倍的二次電子像觀察到但未能在500倍或1000倍的金屬顯微照片中確認之μ相並未包含在μ相的面積率中。這是因為,無法用金屬顯微鏡確認的μ相主要係長邊的長度約為5μm以下、寬度約為0.3μm以下,因此對面積率之影響較小。 Moreover, in the example of changing the average cooling rate, in order to confirm the presence or absence of the μ phase mainly precipitated at the grain boundaries, JSMOL-7000F manufactured by JEOL Ltd. was used at an acceleration voltage of 15 kV and a current value (set value 15) Take a secondary electron image and confirm it at a magnification of 2000 or 5000 Metallographic organization. When the μ phase can be confirmed with a secondary electron image of 2000 or 5000 times, but the μ phase cannot be confirmed with a metal micrograph of 500 or 1000 times, the area ratio is not calculated. That is, the μ phase observed by the secondary electron image at 2000 or 5000 times but not confirmed in the metal micrograph at 500 or 1000 times is not included in the area ratio of the μ phase. This is because the μ phase that cannot be confirmed with a metal microscope mainly has a length of about 5 μm or less and a width of about 0.3 μm or less, and therefore has a small effect on the area ratio.
μ相的長度在任意5個視場中進行測定,如前述那樣將5個視場的最長長度的平均值設為μ相的長邊的長度。μ相的組成確認藉由附屬的EDS進行。再者,當未能以500倍或1000倍確認μ相,但以更高的倍率測定出μ相的長邊的長度時,在表中的測定結果中μ相的面積率雖然為0%,但仍記載有μ相的長邊的長度。 The length of the μ phase is measured in any of the five fields of view, and the average value of the longest length in the five fields of view is the length of the long side of the μ phase as described above. The composition of the μ phase was confirmed by the attached EDS. Furthermore, when the μ phase cannot be confirmed at 500 or 1000 times, but the length of the long side of the μ phase is measured at a higher magnification, the area ratio of the μ phase is 0% in the measurement results in the table. However, the length of the long side of the μ phase is still recorded.
(μ相的觀察) (Observation of μ phase)
關於μ相,若在熱擠壓後或熱處理後,在470℃~380℃的溫度區域以8℃/分鐘或15℃/分鐘以下的平均冷卻速度進行冷卻,則能夠確認μ相的存在。圖1表示試驗No.T05(合金No.S01/製程No.A3)的二次電子像的一例。在α相的晶粒邊界確認到μ相析出(白灰色細長的相)。 About the μ phase, the presence of the μ phase can be confirmed if the μ phase is cooled in a temperature range of 470 ° C. to 380 ° C. at an average cooling rate of 8 ° C./minute or less than 15 ° C./minute after hot extrusion or heat treatment. FIG. 1 shows an example of a secondary electron image of Test No. T05 (Alloy No. S01 / Process No. A3). Precipitation of the μ phase (white-gray slender phase) was confirmed at the grain boundaries of the α-phase.
(存在於α相中之針狀κ相) (Needle-like κ phase present in α phase)
存在於α相中之針狀κ相(κ1相)係寬度為約0.05μm 至約0.5μm,且為細長的直線狀、針狀形態。如果寬度為0.1μm以上,即使用金屬顯微鏡亦能夠確認其存在。 The width of the needle-like κ phase (κ1 phase) existing in the α phase is about 0.05 μm It is about 0.5 μm in length and has a slender, linear, needle-like shape. If the width is 0.1 μm or more, its existence can be confirmed even by using a metal microscope.
圖2表示試驗No.T53(合金No.S02/製程No.A1)的金屬顯微照片作為代表性的金屬顯微照片。圖3表示試驗No.T53(合金No.S02/製程No.A1)的電子顯微照片作為代表性的存在於α相內之針狀κ相的電子顯微照片。再者,圖2、3的觀察位置並不相同。銅合金中,可能與存在於α相之雙晶混淆,但就存在於α相中之κ相而言,κ相自身的寬度窄,雙晶係兩個為1組,因此可以區分它們。在圖2的金屬顯微照片中,可以在α相內觀察到細長直線的針狀圖案的相。在圖3的二次電子像(電子顯微照片)中,明確地確認到存在於α相內之圖案為κ相。κ相的厚度為約0.1~約0.2μm。 FIG. 2 shows a metal photomicrograph of Test No. T53 (Alloy No. S02 / Process No. A1) as a representative metal photomicrograph. FIG. 3 shows an electron micrograph of Test No. T53 (Alloy No. S02 / Process No. A1) as a representative electron micrograph of a needle-like κ phase existing in the α phase. Moreover, the observation positions in FIGS. 2 and 3 are different. In the copper alloy, it may be confused with the twin crystals existing in the α phase, but in the case of the kappa phase existing in the α phase, the width of the kappa phase itself is narrow, and the twin crystal system is two groups, so they can be distinguished. In the metal micrograph of FIG. 2, the phase of the slender straight needle-like pattern can be observed in the α phase. The secondary electron image (electron micrograph) in FIG. 3 clearly confirmed that the pattern existing in the α phase was the κ phase. The κ phase has a thickness of about 0.1 to about 0.2 μm.
用金屬顯微鏡判斷了α相中的針狀κ相的量(數)。在金屬構成相的判定(金相組織觀察)中使用所拍攝之500倍或1000倍倍率下的5個視場的顯微照片。在縱長為約70mm、橫長為約90mm的放大視場中測定針狀κ相的數量,並求出了5個視場的平均值。當針狀κ相的數量在5個視場中的平均值為5以上且小於49時,判斷為具有針狀κ相,並記為“△”。當針狀κ相的數量在5個視場中的平均值超過50時,判斷為具有許多針狀κ相,並記為“○”。當針 狀κ相的數量在5個視場中的平均值為4以下時,判斷為幾乎不具有針狀κ相,並記為“×”。無法用照片確認的針狀κ1相的數量並未包含在內。 The amount (number) of acicular κ phases in the α phase was determined with a metal microscope. In the determination of the metal constituent phase (metallographic observation), photomicrographs of 5 fields of view taken at 500 or 1000 times magnification were used. The number of needle-like kappa phases was measured in an enlarged field of view having a length of about 70 mm and a width of about 90 mm, and an average value of 5 fields of view was obtained. When the average of the number of acicular κ phases in 5 fields of view is 5 or more and less than 49, it is judged that the acicular κ phase has the acicular κ phase, and is recorded as "Δ". When the average of the number of acicular κ phases in the five fields of view exceeds 50, it is judged that there are many acicular κ phases, and it is recorded as "○". When the needle When the average of the number of κ-phases in the 5 fields of view is 4 or less, it is determined that there is almost no needle-shaped κ-phases, and it is described as “×”. The number of acicular κ1 phases that cannot be confirmed with photos is not included.
(κ相中所含之Sn量、P量) (Sn amount, P amount contained in κ phase)
使用X射線微分析器測定了κ相中所含之Sn量、P量。 測定時使用JEOL Ltd.製造的“JXA-8200”,在加速電壓20kV、電流值3.0×10-8A的條件下進行。 The amount of Sn and P contained in the κ phase were measured using an X-ray microanalyzer. The measurement was carried out using "JXA-8200" manufactured by JEOL Ltd., under the conditions of an acceleration voltage of 20 kV and a current value of 3.0 × 10 -8 A.
關於試驗No.T03(合金No.S01/製程No.A1)、試驗No.T25(合金No.S01/製程No.BH3)、試驗No.T229(合金No.S20/製程No.EH1)、試驗No.T230(合金No.S20/製程No.E1),使用X射線微分析器對各相的Sn、Cu、Si、P的濃度進行定量分析之結果示於表13~表16。 Test No.T03 (Alloy No.S01 / Process No.A1), Test No.T25 (Alloy No.S01 / Process No.BH3), Test No.T229 (Alloy No.S20 / Process No.EH1), Test Table 13 to Table 16 show the results of quantitative analysis of the concentrations of Sn, Cu, Si, and P in each phase using X-ray microanalyzer No. T230 (Alloy No. S20 / Process No. E1).
關於μ相,利用附屬於JSM-7000F的EDS進行測定,並測定了在視場內短邊的長度較大的部分。 The μ phase was measured using an EDS attached to JSM-7000F, and a portion with a large short side length in the field of view was measured.
由上述測定結果得到如下見解。 The following findings were obtained from the above measurement results.
1)藉由合金組成而分佈於各相之濃度略有不同。 1) The concentration distributed in each phase is slightly different depending on the alloy composition.
2)Sn在κ相中的分佈為α相的約1.4倍。 2) The distribution of Sn in the κ phase is about 1.4 times that of the α phase.
3)γ相的Sn濃度為α相的Sn濃度的約10~約15倍。 3) The Sn concentration in the γ phase is about 10 to about 15 times the Sn concentration in the α phase.
4)與α相的Si濃度相比,κ相、γ相、μ相的Si濃度分別約為1.5倍、約2.2倍、約2.7倍。 4) Compared with the Si concentration of the α phase, the Si concentrations of the κ phase, γ phase, and μ phase are about 1.5 times, about 2.2 times, and about 2.7 times, respectively.
5)μ相的Cu濃度高於α相、κ相、γ相、μ相。 5) The Cu concentration of μ phase is higher than that of α phase, κ phase, γ phase, and μ phase.
6)若γ相的比例增加,則κ相的Sn濃度必然減少。 6) If the proportion of the γ phase is increased, the Sn concentration of the κ phase is necessarily reduced.
7)P在κ相中的分佈為α相的約2倍。 7) The distribution of P in the κ phase is approximately twice that of the α phase.
8)γ相的P濃度為α相的P濃度的約3倍,μ相的P濃度為α相的P濃度的約4倍。 8) The P concentration in the γ phase is about 3 times the P concentration in the α phase, and the P concentration in the μ phase is about 4 times the P concentration in the α phase.
9)即使為相同組成,若γ相的比例減少,則α相的Sn濃度從0.13mass%至0.22mass%提高約1.7倍(合金No.S20)。同樣地,κ相的Sn濃度從0.18mass%至0.31mass%提高約1.7倍。又,若γ相的比例減少,則α相的Sn濃度從0.13mass%至0.18mass%增加0.05mass%,κ相的Sn濃度從0.22mass%至0.31mass%增加0.09mass%。κ相的Sn的增加量超過α相的Sn的增加量。 9) Even with the same composition, if the ratio of the γ phase is reduced, the Sn concentration of the α phase is increased by about 1.7 times from 0.13 mass% to 0.22 mass% (Alloy No. S20). Similarly, the Sn concentration of the kappa phase increased by about 1.7 times from 0.18 mass% to 0.31 mass%. When the proportion of the γ phase decreases, the Sn concentration of the α phase increases from 0.13 mass% to 0.18 mass% by 0.05 mass%, and the Sn concentration of the κ phase increases from 0.22 mass% to 0.31 mass% by 0.09 mass%. The increase amount of Sn in the κ phase exceeds the increase amount of Sn in the α phase.
(機械特性) (Mechanical characteristics)
(抗拉強度) (tensile strength)
將各試驗材料加工成JIS Z 2241的10號試片,從而進行了抗拉強度的測定。如果熱擠出材料或熱鍛造材料的抗拉強度為530N/mm2以上(較佳為550N/mm2以上),則在易削性銅合金中亦為最高水準,能夠實現在各領域中使用之構件的薄壁化/輕量化。 Each test material was processed into No. 10 test piece of JIS Z 2241, and the tensile strength was measured. If the tensile strength of the hot forging or hot extrusion material material is 530N / mm 2 or more (preferably 550N / mm 2 or more), it is easy to cut copper in the alloy is also the highest level, it is possible to use in various fields Thinner and lighter components.
再者,抗拉試片的完工面粗糙度影響伸長率和抗拉強 度。因此,以滿足下述條件之方式製作出抗拉試片。 Furthermore, the roughness of the finished surface of the tensile test piece affects the elongation and tensile strength. degree. Therefore, a tensile test piece was produced so as to satisfy the following conditions.
(抗拉試片的完工面粗糙度的條件) (Conditions of Roughness of Finished Surface of Tensile Test Strip)
在抗拉試片的標點間的任意位置的每基準長度4mm的截面曲線中,Z軸的最大值與最小值之差為2μm以下。截面曲線係指,將截止值λ s的低通濾波器適用於測定截面曲線而得之曲線。 In a cross-sectional curve of 4 mm per reference length at any position between the punctuation points of the tensile test piece, the difference between the maximum value and the minimum value of the Z axis is 2 μm or less. The cross-sectional curve refers to a curve obtained by applying a low-pass filter having a cutoff value λ s to a cross-sectional curve.
(高溫潛變) (High temperature creep)
根據各試片製作出JIS Z 2271的直徑10mm之帶法蘭的試片。測定了在將相當於室溫的0.2%保證應力之荷載施加於試片之狀態下,於150℃經過100小時後的潛變應變。 以常溫下的標點間的伸長率施加相當於0.2%的塑性變形之荷載,如果在施加了該荷載之狀態下將試片於150℃保持100小時之後的潛變應變為0.4%以下,則為良好。如果該潛變應變為0.3%以下,則為銅合金中的最高水準,例如,能夠在高溫下使用之閥、靠近發動機室的汽車組件中,用作可靠性高的材料。 A flanged test piece with a diameter of 10 mm in accordance with JIS Z 2271 was produced from each test piece. The creep strain after 100 hours at 150 ° C was measured in a state where a load corresponding to a guaranteed stress of 0.2% of room temperature was applied to the test piece. A load equivalent to 0.2% of plastic deformation is applied at the elongation between the punctuation points at normal temperature. If the test piece is held at 150 ° C for 100 hours under the load, the creep strain is 0.4% or less. good. If the creep strain is 0.3% or less, it is the highest level among copper alloys. For example, it can be used as a highly reliable material in valves that can be used at high temperatures and in automotive components close to the engine room.
(衝擊特性) (Impact characteristics)
在衝擊試驗中,從擠壓棒材、鍛造材料及其替代材料、鑄造材料、連續鑄造棒材中選取了依照JIS Z 2242之U形凹口試片(凹口深度2mm、凹口底部半徑1mm)。用半徑2mm的衝擊刃進行夏比衝擊試驗,並測定了衝擊值。 In the impact test, a U-shaped notch test piece (notch depth 2mm, notch bottom radius 1mm) according to JIS Z 2242 was selected from extruded bars, forged materials and their alternative materials, casting materials, and continuous casting bars. . A Charpy impact test was performed with an impact blade having a radius of 2 mm, and the impact value was measured.
再者,用V凹口試片和U形凹口試片進行時的衝擊值 的關係大致如下。 In addition, the impact value when using a V-notch test piece and a U-notch test piece The relationship is roughly as follows.
(V凹口衝擊值)=0.8×(U形凹口衝擊值)-3 (V-notch impact value) = 0.8 × (U-shaped notch impact value) -3
(切削性) (Machinability)
作為切削性的評價,如下對使用了車床之切削試驗進行了評價。 As the evaluation of the machinability, the cutting test using a lathe was evaluated as follows.
對直徑50mm、40mm或25.6mm的熱擠壓棒材、直徑25mm(24.4mm)的冷拉伸材料實施切削加工而製作出直徑18mm之試驗材料。對鍛造材料實施切削加工而製作出直徑14.5mm之試驗材料。將尖頭直鋒刀具(point nose straight tool),尤其將不帶斷屑槽之碳化鎢刀具安裝在車床上。使用該車床,於乾式條件下,並在前刀角-6度、刀尖半徑0.4mm、切削速度150m/分鐘、切削深度1.0mm、進給速度0.11mm/rev的條件下,在直徑18mm或直徑14.5mm的試驗材料的圓周上進行了切割。 Hot-extruded rods with a diameter of 50mm, 40mm, or 25.6mm, and cold-drawn materials with a diameter of 25mm (24.4mm) were cut to produce test materials with a diameter of 18mm. The forged material was cut to produce a test material with a diameter of 14.5 mm. A point nose straight tool, especially a tungsten carbide tool without chip breaker, is installed on the lathe. Using this lathe, under dry conditions, under the conditions of a rake angle of -6 degrees, a cutting edge radius of 0.4mm, a cutting speed of 150m / min, a cutting depth of 1.0mm, and a feed speed of 0.11mm / rev, the diameter is 18mm or The test material with a diameter of 14.5 mm was cut on the circumference.
從包括安裝於工具之3個部分之測力計(三保電機製作所製造,AST式工具測力計AST-TL1003)發出之信號轉換為電氣電壓信號(electrical voltage signal),並記錄在記錄器中。接著,該等信號被轉換為切削阻力(N)。因此,藉由測定切削阻力尤其是在切削時顯示最高值之主分力,對合金的切削性進行了評價。 A signal from an dynamometer (manufactured by Miho Electric Manufacturing Co., Ltd., AST-type tool dynamometer AST-TL1003) including three parts mounted on the tool is converted into an electrical voltage signal and recorded in a recorder. These signals are then converted into cutting resistance (N). Therefore, the machinability of the alloy was evaluated by measuring the main component force that showed the highest value in cutting resistance, particularly during cutting.
同時選取切屑,並藉由切屑形狀對切削性進行了評價。在實際使用的切割中成為最大問題的是,切屑纏上工具或 切屑的體積較大。因此,將只產生切屑形狀為1卷以下的切屑的情況評價為“○”(good(良好))。將產生切屑形狀超過1卷且3卷為止的切屑的情況評價為“△”(fair(尚可))。將產生切屑形狀超過3卷之切屑的情況評價為“×”(poor(不良))。這樣,進行了3個階段的評價。 At the same time, chips were selected and the machinability was evaluated based on the chip shape. The biggest problem in practical cutting is that the chips are wrapped in tools or The chip volume is large. Therefore, a case where only chips having a chip shape of 1 roll or less was generated was evaluated as “○” (good). A case where chips having a chip shape exceeding 1 roll and 3 rolls were evaluated was "Δ" (fair). A case where chips having a chip shape exceeding three rolls were evaluated was evaluated as “×” (poor). In this way, evaluation was performed in three stages.
切削阻力還依賴於材料的強度,例如剪斷應力、抗拉強度和0.2%保證應力,具有強度越高的材料切削阻力越高之傾向。如果與含有1~4%的Pb之易削黃銅棒的切削阻力相比,切削阻力高出約10%至約20%的程度,則在實際使用上被充分容許。本實施形態中,以130N為界(邊界值)來對切削阻力進行了評價。詳細而言,若切削阻力小於130N,則評價為切削性優異(評價:○)。若切削阻力為130N以上且小於150N,則將切削性評價為“尚可(△)”。 若切削阻力為150N以上,則評價為“不良(×)”。另外,對58mass%Cu-42mass%Zn合金實施製程No.F1來製作試樣並進行了評價的結果,切削阻力為185N。 Cutting resistance also depends on the strength of the material, such as shear stress, tensile strength and 0.2% guaranteed stress. The higher the strength, the higher the cutting resistance of the material. If the cutting resistance is about 10% to about 20% higher than the cutting resistance of a free-cutting brass rod containing 1 to 4% of Pb, it is sufficiently tolerated in practical use. In the present embodiment, the cutting resistance was evaluated with a boundary (boundary value) of 130N. Specifically, if the cutting resistance is less than 130N, it is evaluated that the machinability is excellent (evaluation: ○). When the cutting resistance is 130N or more and less than 150N, the machinability is evaluated as "OK (Δ)". When the cutting resistance was 150 N or more, it was evaluated as "defective (×)". In addition, 58 mass% Cu-42mass% Zn alloy was produced by process No. F1 to prepare a sample and evaluated. As a result, the cutting resistance was 185N.
作為綜合性的切削性的評價,將切屑形狀良好(評價:○)且切削阻力低的(評價:○)評價為切削性優異(excellent(極好))。當切屑形狀和切削阻力中的一者為△或尚可的情況下,附帶條件地評價為切削性良好(good)。 當切屑形狀和切削阻力中的一者為△或尚可,另一者為×或不良的情況下,評價為切削性不良(poor)。 As a comprehensive evaluation of the machinability, the chip shape was good (evaluation: ○) and the cutting resistance was low (evaluation: ○) as being excellent in machinability (excellent). When one of the chip shape and the cutting resistance is Δ or acceptable, the cutting condition is evaluated to be good. When one of the chip shape and the cutting resistance was Δ or acceptable, and the other was × or poor, it was evaluated as poor cutting.
(熱加工試驗) (Hot working test)
將直徑50mm、直徑40mm、直徑25.6mm或直徑25.0mm的棒材藉由切割而使其成為直徑15mm,並切斷成長度25mm來製作出試驗材料。將試驗材料於740℃或635℃保持了20分鐘。繼而,縱向放置試驗材料,並使用以10噸的熱壓縮能力併設有電爐之Amsler試驗機,在應變速度0.02/秒、加工率80%下進行高溫壓縮,從而使厚度成為5mm。 A test material was produced by cutting a rod having a diameter of 50 mm, a diameter of 40 mm, a diameter of 25.6 mm, or a diameter of 25.0 mm into a diameter of 15 mm, and cutting it into a length of 25 mm. The test material was held at 740 ° C or 635 ° C for 20 minutes. Next, the test material was placed vertically, and an Amsler tester equipped with an electric furnace with a thermal compression capacity of 10 tons was used to perform high-temperature compression at a strain rate of 0.02 / second and a processing rate of 80%, so that the thickness became 5 mm.
關於熱加工性的評價,當使用10倍倍率的放大鏡觀察到0.2mm以上開口之破裂時,判斷為產生破裂。將在740℃、635℃這兩個條件下均未產生破裂的情況評價為“○”(good)。將在740℃產生了破裂但在635℃未產生破裂的情況評價為“△”(fair)。將在740℃未產生破裂但在635℃產生了破裂的情況評價為“▲”(fair)。將在740℃、635℃這兩個條件下均產生破裂的情況評價為“×”(poor)。 Regarding the evaluation of hot workability, when a crack of an opening of 0.2 mm or more was observed using a 10-fold magnifying glass, it was judged that cracking occurred. A case where cracking did not occur under both conditions of 740 ° C and 635 ° C was evaluated as "Good" (good). A case where a crack occurred at 740 ° C but no crack occurred at 635 ° C was evaluated as "Δ" (fair). A case where no crack occurred at 740 ° C but a crack occurred at 635 ° C was evaluated as "▲" (fair). A case where cracking occurred under both conditions of 740 ° C and 635 ° C was evaluated as "poor".
在740℃、635℃這兩個條件下均未產生破裂時,關於實際使用上的熱擠壓及熱鍛造,就實施方面而言,即使發生一些材料溫度下降,又,即使金屬模或鑄模與材料雖是瞬時但有接觸且材料的溫度下降,只要在適當的溫度實施則在實際使用上沒有問題。當在740℃和635℃中的任一溫度產生破裂時,雖然受到實際使用上的限制,但只要以更窄的溫度範圍進行管理,則判斷為可以實施熱加工。當在740℃和635℃這兩種溫度均產生破裂時,判斷為實際使用 上存在問題。 When cracking does not occur under both conditions of 740 ° C and 635 ° C, regarding the hot extrusion and hot forging in actual use, as far as the implementation is concerned, even if the temperature of some materials drops, Although the material is instant but has contact and the temperature of the material decreases, as long as it is implemented at an appropriate temperature, there is no problem in practical use. When cracking occurs at any of 740 ° C and 635 ° C, although it is limited in practical use, as long as it is managed in a narrower temperature range, it is determined that hot working can be performed. When cracking occurs at both temperatures of 740 ° C and 635 ° C, it is judged as practical use There is a problem.
(脫鋅腐蝕試驗1、2) (Dezincification corrosion test 1, 2)
當試驗材料為擠出材料時,以使試驗材料的曝露試樣表面與擠出方向垂直之方式,將試驗材料植入酚醛樹脂材料中。當試驗材料為鑄件材料(鑄造棒)時,以使試驗材料的曝露試樣表面與鑄件材料的長邊方向垂直之方式,將試驗材料植入酚醛樹脂材料中。當試驗材料為鍛造材料時,以使試驗材料的曝露試樣表面與鍛造的流動方向垂直之方式植入酚醛樹脂材料中。 When the test material is an extruded material, the test material is implanted into the phenolic resin material such that the surface of the exposed sample of the test material is perpendicular to the extrusion direction. When the test material is a casting material (casting rod), the test material is implanted into the phenol resin material so that the surface of the exposed sample of the test material is perpendicular to the longitudinal direction of the casting material. When the test material is a forged material, the phenolic resin material is implanted so that the surface of the exposed sample of the test material is perpendicular to the forging flow direction.
將試樣表面藉由至1200號的金鋼砂紙進行研磨,繼而,在純水中進行超音波清洗並用鼓風機進行乾燥。之後,將各試樣浸漬於所準備之浸漬液中。 The surface of the sample was ground with a gold-steel sandpaper up to No. 1200, followed by ultrasonic cleaning in pure water and drying with a blower. Then, each sample was immersed in the prepared immersion liquid.
試驗結束後,以使曝露表面與擠出方向、長邊方向或鍛造的流動方向保持垂直之方式,將試樣再次植入到酚醛樹脂材料中。接著,以使腐蝕部的截面作為最長的切斷部而獲得之方式切斷試樣。接著對試樣進行了研磨。 After the test, the sample was re-implanted into the phenol resin material so that the exposed surface was perpendicular to the extrusion direction, the long-side direction, or the forging flow direction. Next, the sample was cut so that the cross section of the corroded part was obtained as the longest cut part. The sample was then ground.
使用金屬顯微鏡,以500倍的倍率在顯微鏡的10個視場(任意的10個視場)中對腐蝕深度進行了觀察。最深的腐蝕點被記錄為最大脫鋅腐蝕深度。 Using a metal microscope, the depth of corrosion was observed in 10 microscope fields (arbitrary 10 fields) at a magnification of 500 times. The deepest corrosion point is recorded as the maximum dezincification corrosion depth.
在脫鋅腐蝕試驗1中,作為浸漬液,準備了以下試驗液1,並實施了上述操作。在脫鋅腐蝕試驗2中,作為浸漬液,準備了以下試驗液2,並實施了上述操作。 In the dezincification corrosion test 1, the following test liquid 1 was prepared as an immersion liquid, and the above operation was performed. In the dezincification corrosion test 2, the following test liquid 2 was prepared as an immersion liquid, and the above operation was performed.
試驗液1為用於假設投入過量的作為氧化劑之消毒劑且pH低的惡劣的腐蝕環境,進而在該腐蝕環境下進行加速試驗之溶液。若使用該溶液,則推測加速試驗將成為該惡劣的腐蝕環境下的約75~100倍。若最大腐蝕深度為70μm以下,則耐蝕性良好。在要求優異之耐蝕性時,推測最大腐蝕深度較佳為50μm以下,進一步較佳為30μm以下即可。 The test solution 1 is a solution for assuming a severely corrosive environment with a low pH as a disinfectant as an oxidant, and further performing an accelerated test under the corrosive environment. If this solution is used, it is estimated that the accelerated test will be about 75 to 100 times that in the severe corrosive environment. When the maximum corrosion depth is 70 μm or less, the corrosion resistance is good. When excellent corrosion resistance is required, it is estimated that the maximum corrosion depth is preferably 50 μm or less, and more preferably 30 μm or less.
試驗液2為用於假設氯化物離子濃度高、pH低的惡劣的腐蝕環境的水質,進而在該腐蝕環境下進行加速試驗之溶液。若使用該溶液,則推測加速試驗將成為在該惡劣的腐蝕環境下的約30~50倍。若最大腐蝕深度為40μm以下,則耐蝕性良好。在要求優異之耐蝕性時,推測最大腐蝕深度較佳為30μm以下,進一步較佳為20μm以下即可。本實施例中,基於該等推測值來進行了評價。 The test solution 2 is a solution for assuming a harsh corrosive environment with a high chloride ion concentration and a low pH, and further performing an accelerated test under the corrosive environment. If this solution is used, it is estimated that the accelerated test will be approximately 30 to 50 times in this severe corrosive environment. When the maximum corrosion depth is 40 μm or less, the corrosion resistance is good. When excellent corrosion resistance is required, it is estimated that the maximum corrosion depth is preferably 30 μm or less, and more preferably 20 μm or less. In this example, evaluation was performed based on these estimated values.
脫鋅腐蝕試驗1中,作為試驗液1,使用了次氯酸水(濃度30ppm、pH=6.8、水溫40℃)。藉由以下方法對試驗液1進行了調整。向蒸餾水40L中投入市售之次氯酸鈉(NaClO),並以藉由碘滴定法產生之殘留氯濃度成為30mg/L之方式進行了調整。殘留氯隨著時間而分解並減少,因此藉由伏安法時常測定殘留氯濃度,並且藉由電磁泵對次氯酸鈉的投入量進行了電子控制。為了將pH降低至6.8,一邊對二氧化碳進行流量調整一邊進行投入。利用溫度控制器對水溫進行調整以使其成為40℃。這樣,將殘留氯濃 度、pH、水溫保持恆定,並且在試驗液1中將試樣保持了兩個月。繼而從水溶液中取出試樣,並測定了其脫鋅腐蝕深度的最大值(最大脫鋅腐蝕深度)。 In the dezincification corrosion test 1, as the test liquid 1, hypochlorous acid water (concentration: 30 ppm, pH = 6.8, water temperature: 40 ° C) was used. The test liquid 1 was adjusted by the following method. Commercially available sodium hypochlorite (NaClO) was added to 40 L of distilled water, and adjusted so that the residual chlorine concentration by the iodine titration method became 30 mg / L. Residual chlorine decomposes and decreases with time. Therefore, the residual chlorine concentration is often measured by voltammetry, and the amount of sodium hypochlorite input is electronically controlled by an electromagnetic pump. In order to lower the pH to 6.8, the carbon dioxide was adjusted while the flow rate was adjusted. The temperature of the water was adjusted by a temperature controller to 40 ° C. In this way, the residual chlorine is concentrated The temperature, pH, and water temperature were kept constant, and the sample was held in the test solution 1 for two months. Then, the sample was taken out from the aqueous solution, and the maximum value of the dezincification corrosion depth (maximum dezincification corrosion depth) was measured.
在脫鋅腐蝕試驗2中,作為試驗液2,使用了表17所示之成分的試驗水。向蒸餾水中投入市售之藥劑而對試驗液2進行了調整。假設腐蝕性高的自來水管,並投入了氯化物離子80mg/L、硫酸根離子40mg/L及硝酸根離子30mg/L。鹼度及硬度以日本一般的自來水管為基準分別調整為30mg/L、60mg/L。為了將pH降低至6.3,一邊對二氧化碳進行流量調整一邊進行投入,為了使溶氧濃度飽和,時常投入了氧氣。水溫與室溫相同,於25℃進行。這樣,將pH、水溫保持恆定並將溶氧濃度設為飽和狀態,並且在試驗液2中將試樣保持了三個月。繼而,從水溶液中取出試樣,並測定了其脫鋅腐蝕深度的最大值(最大脫鋅腐蝕深度)。 In the dezincification corrosion test 2, as the test liquid 2, test water having a composition shown in Table 17 was used. The test solution 2 was adjusted by putting a commercially available drug into distilled water. It is assumed that a highly corrosive water pipe is charged with 80 mg / L of chloride ion, 40 mg / L of sulfate ion, and 30 mg / L of nitrate ion. The alkalinity and hardness were adjusted to 30mg / L and 60mg / L, respectively, based on the general Japanese water pipe. In order to lower the pH to 6.3, the carbon dioxide was injected while adjusting the flow rate of carbon dioxide, and oxygen was often injected to saturate the dissolved oxygen concentration. The water temperature was the same as room temperature, and it was performed at 25 ° C. In this way, the pH and water temperature were kept constant, and the dissolved oxygen concentration was set to a saturated state, and the sample was held in the test solution 2 for three months. Then, the sample was taken out from the aqueous solution, and the maximum value (maximum dezincification corrosion depth) of the dezincification corrosion depth was measured.
(脫鋅腐蝕試驗3:ISO6509脫鋅腐蝕試驗) (Dezincification corrosion test 3: ISO6509 dezincification corrosion test)
本試驗作為脫鋅腐蝕試驗方法而被諸多國家所採用,在JIS標準中亦以JIS H 3250規定。 This test is used in many countries as a method of dezincification corrosion test, and it is also specified in JIS H 3250 in the JIS standard.
與脫鋅腐蝕試驗1、2相同地將試驗材料植入了酚醛樹脂材料中。例如以使曝露試樣表面與擠出材料的擠出方向垂直之方式植入酚醛樹脂材料中。將試樣表面藉由至1200號的金鋼砂紙進行研磨,繼而,在純水中進行超音波清洗並進行了乾燥。 The test material was implanted into the phenol resin material in the same manner as in the dezincification corrosion test 1 and 2. For example, the exposed sample surface is implanted into the phenol resin material such that the surface of the exposed sample is perpendicular to the extrusion direction of the extruded material. The surface of the sample was polished with gold-steel sandpaper up to No. 1200, and then ultrasonically washed in pure water and dried.
將各試樣浸漬於1.0%的氯化銅二水和鹽(CuCl2.2H2O)的水溶液(12.7g/L)中,在75℃的溫度條件下保持了24小時。之後,從水溶液中取出試樣。 Each sample was immersed in an aqueous solution (12.7 g / L) of 1.0% copper chloride dihydrate and a salt (CuCl 2 .2H 2 O), and maintained at a temperature of 75 ° C. for 24 hours. After that, the sample was taken out of the aqueous solution.
以使曝露表面與擠出方向、長邊方向或鍛造的流動方向保持垂直之方式,將試樣再次植入到酚醛樹脂材料中。 接著,以使腐蝕部的截面作為最長的切斷部而獲得之方式切斷試樣。接著對試樣進行了研磨。 The specimen was re-implanted into the phenolic resin material such that the exposed surface was perpendicular to the direction of extrusion, the direction of the long side, or the direction of the flow of the forging. Next, the sample was cut so that the cross section of the corroded part was obtained as the longest cut part. The sample was then ground.
使用金屬顯微鏡,以100倍~500倍的倍率在顯微鏡的10個視場中對腐蝕深度進行了觀察。最深的腐蝕點被記錄為最大脫鋅腐蝕深度。 Using a metal microscope, the depth of corrosion was observed in 10 fields of view of the microscope at a magnification of 100 to 500 times. The deepest corrosion point is recorded as the maximum dezincification corrosion depth.
再者,當進行ISO 6509的試驗時,若最大腐蝕深度為200μm以下,則成為在實際使用上對耐蝕性沒有問題的水準。尤其在要求優異之耐蝕性時,設為最大腐蝕深度較佳為100μm以下,進一步較佳為50μm以下。 In addition, when the test of ISO 6509 is performed, if the maximum corrosion depth is 200 μm or less, it becomes a level that has no problem with corrosion resistance in practical use. In particular, when excellent corrosion resistance is required, the maximum corrosion depth is preferably 100 μm or less, and more preferably 50 μm or less.
本試驗中,將最大腐蝕深度超過200μm的情況評價為“×”(poor)。將最大腐蝕深度超過50μm且200μm以下的情況評價為“△”(fair)。將最大腐蝕深度為50μm以下的 情況嚴格地評價為“○”(good)。本實施形態為了假設惡劣的腐蝕環境而採用了嚴格的評價基準,僅將評價為“○”的情況視為耐蝕性良好。 In this test, a case where the maximum corrosion depth exceeds 200 μm is evaluated as “poor”. A case where the maximum corrosion depth exceeds 50 μm and 200 μm or less is evaluated as “fair”. The maximum corrosion depth is 50 μm or less The situation was strictly evaluated as "○" (good). In the present embodiment, strict evaluation criteria are adopted in order to assume a severe corrosive environment, and only a case where the evaluation is "○" is regarded as a good corrosion resistance.
(磨耗試驗) (Abrasion test)
藉由在潤滑條件下的Amsler型磨耗試驗及在乾式條件下的球盤(ball-on-disk)摩擦磨耗試驗這兩種試驗,對耐磨耗性進行了評價。所使用之試樣為在製程No.C0、C1、CH1、E2、E3中製作出之合金。 The abrasion resistance was evaluated by two tests, an Amsler type abrasion test under lubricating conditions and a ball-on-disk friction abrasion test under dry conditions. The samples used were alloys made in process Nos. C0, C1, CH1, E2, and E3.
藉由以下方法實施了Amsler型磨耗試驗。於室溫下對各樣品進行切削加工而使其直徑成為32mm從而製作出上部試片。又,準備了沃斯田鐵不銹鋼(JIS G 4303的SUS304)製造的直徑42mm的下部試片(表面硬度HV184)。作為荷載施加490N而使上部試片和下部試片接觸。油滴和油浴使用了矽油。在施加荷載而使上部試片和下部試片接觸之狀態下,以上部試片的轉速(旋轉速度)為188rpm、下部試片的轉速(旋轉速度)為209rpm之條件使上部試片和下部試片旋轉。利用上部試片和下部試片的圓周速度差來將滑動速度設為0.2m/sec。藉由上部試片和下部試片的直徑及轉速(旋轉速度)不同,使試片磨損。使上部試片和下部試片進行旋轉直至下部試片的旋轉次數成為250000次。 An Amsler type abrasion test was performed by the following method. Each sample was cut at room temperature so that the diameter became 32 mm, and an upper test piece was produced. In addition, a lower test piece (surface hardness HV184) with a diameter of 42 mm manufactured by Vostian Iron Stainless Steel (SUS304 of JIS G 4303) was prepared. A load of 490 N was applied to bring the upper and lower test pieces into contact. Oil droplets and oil baths use silicone oil. In a state where the upper test piece and the lower test piece are brought into contact with a load, the upper test piece and the lower test piece have a rotation speed (rotation speed) of 188 rpm and a lower test piece rotation speed (rotation speed) of 209 rpm. Slice rotation. The slip speed was set to 0.2 m / sec using the peripheral speed difference between the upper and lower test pieces. As the diameter and the rotation speed (rotation speed) of the upper test piece and the lower test piece are different, the test piece is worn. The upper test piece and the lower test piece were rotated until the number of rotations of the lower test piece reached 250,000 times.
試驗後,測定上部試片的重量變化,並藉由以下基準對耐磨耗性進行了評價。將由磨耗產生之上部試片的重量 的減少量為0.25g以下的情況評價為“◎”(excellent)。將上部試片的重量的減少量超過0.25g且0.5g以下的情況評價為“○”(good)。將上部試片的重量的減少量超過0.5g且1.0g以下的情況評價為“△”(fair)。將上部試片的重量的減少量超過1.0g的情況評價為“×”(poor)。藉由該四個階段對耐磨耗性進行了評價。再者,在下部試片中,當存在0.025g以上的磨耗減量的情況評價為“×”。 After the test, the weight change of the upper test piece was measured, and the abrasion resistance was evaluated by the following criteria. The weight of the upper test piece will be generated by abrasion When the amount of reduction was 0.25 g or less, it was evaluated as "excellent". The case where the weight reduction of the upper test piece exceeded 0.25 g and 0.5 g or less was evaluated as "Good" (good). The case where the weight loss of the upper test piece was more than 0.5 g and 1.0 g or less was evaluated as “Δ” (fair). The case where the weight reduction of the upper test piece exceeded 1.0 g was evaluated as "poor". The abrasion resistance was evaluated through these four stages. In addition, in the lower test piece, when abrasion loss of 0.025 g or more was present, it was evaluated as “×”.
另外,含有同一試驗條件下的59Cu-3Pb-38Zn的Pb之易削黃銅的磨耗減量(由磨耗產生之重量的減少量)為12g。 In addition, the abrasion loss (amount of weight reduction due to abrasion) of free-cutting brass containing 59Cu-3Pb-38Zn Pb under the same test conditions was 12 g.
藉由以下方法實施了球盤摩擦磨耗試驗。用粗糙度#2000的砂紙對試片的表面進行了研磨。在藉由以下條件將沃斯田鐵不銹鋼(JIS G 4303的SUS304)製直徑10mm的鋼球推到該試片上之狀態下進行滑動。 A ball-disk friction abrasion test was performed by the following method. The surface of the test piece was polished with a sandpaper of roughness # 2000. A steel ball with a diameter of 10 mm made by Vostian Iron Stainless Steel (SUS304 of JIS G 4303) was pushed onto the test piece under the following conditions and slid.
(條件) (condition)
室溫、無潤滑、荷載:49N、滑動直徑:直徑10mm、滑動速度:0.1m/sec、滑動距離:120m。 Room temperature, non-lubricated, load: 49N, sliding diameter: 10mm in diameter, sliding speed: 0.1m / sec, sliding distance: 120m.
試驗後,測定試片的重量變化,並藉由以下基準對耐磨耗性進行了評價。將由磨耗產生之試片重量的減少量為4mg以下的情況評價為“◎”(excellent)。將試片重量的減少量超過4mg且8mg以下的情況評價為“○”(good)。 將試片重量的減少量超過8mg且20mg以下的情況評價為“△”(fair)。將試片重量的減少量超過20mg的情況評價 為“×”(poor)。藉由該四個階段對耐磨耗性進行了評價。 After the test, the weight change of the test piece was measured, and the abrasion resistance was evaluated by the following criteria. The case where the weight reduction of the test piece by abrasion was 4 mg or less was evaluated as "excellent". A case where the weight of the test piece was reduced to more than 4 mg and 8 mg or less was evaluated as "Good" (good). A case where the weight of the test piece was reduced to more than 8 mg and less than 20 mg was evaluated as “fair”. Evaluation of a case where the weight of the test piece is reduced by more than 20 mg "X" (poor). The abrasion resistance was evaluated through these four stages.
另外,含有同一試驗條件下的59Cu-3Pb-38Zn的Pb之易削黃銅的磨耗減量為80mg。 In addition, the abrasion loss of free-cutting brass containing Pb of 59Cu-3Pb-38Zn under the same test conditions was 80 mg.
將評價結果示於表18~表47。 The evaluation results are shown in Tables 18 to 47.
試驗No.T01~T98、T101~T150為實際操作的實驗中的結果。試驗No.T201~T258、T301~T308為相當於實驗室的實驗中的實施例的結果。試驗No.T501~T546為相當於實驗室的實驗中的比較例的結果。 Test Nos. T01 to T98 and T101 to T150 are the results of actual experiments. Test Nos. T201 to T258 and T301 to T308 are results corresponding to examples in laboratory experiments. Test Nos. T501 to T546 are results corresponding to comparative examples in laboratory experiments.
表中的製程No.中記載的“*1”表示係以下事項。 "* 1" described in the process number in the table indicates the following matters.
*1)使用EH1材料實施了熱加工性的評價。 * 1) Evaluation of hot workability was performed using EH1 material.
又,關於製程No.中記載為“EH1、E2”或“E1、E3”之試驗,使用在製程No.E2或E3中製作之試樣來實施了磨耗試驗。使用在製程No.EH1或E1中製作之試樣來實施了除磨耗試驗以外之腐蝕試驗、機械性質等所有試驗及金相組織的調查。 In addition, regarding the test described as "EH1, E2" or "E1, E3" in the process number, the abrasion test was implemented using the sample produced in process number E2 or E3. The samples prepared in Process No. EH1 or E1 were used to perform all tests except corrosion tests, mechanical properties, and other investigations, as well as investigation of metallographic structure.
以上實驗結果總結如下。 The above experimental results are summarized as follows.
1)能夠確認藉由滿足本實施形態的組成,並滿足組成關係式f1、f2、金相組織的要件及組織關係式f3、f4、f5、f6,從而藉由含有少量的Pb而得到良好的切削性,並得到具備良好的熱加工性、惡劣的環境下的優異之耐蝕性,且帶有高強度、良好的衝擊特性、耐磨耗性及高溫特性之熱擠出材料、熱鍛造材料(例如,合金No.S01、S02、13,製程No.A1、C1、D1、E1、F1、F3)。 1) It can be confirmed that by satisfying the composition of this embodiment, and satisfying the compositional relations f1, f2, the requirements of the metallurgical structure and the organization relational expressions f3, f4, f5, and f6, a good content is obtained by containing a small amount of Pb Machinability and hot extruded materials and hot forged materials with good hot workability and excellent corrosion resistance in harsh environments, with high strength, good impact characteristics, abrasion resistance and high temperature characteristics ( For example, alloy No. S01, S02, and 13, process No. A1, C1, D1, E1, F1, F3).
2)能夠確認含有Sb、As進一步提高了惡劣的條件下的耐蝕性(合金No.S41~S45)。 2) It can be confirmed that the inclusion of Sb and As further improves the corrosion resistance under severe conditions (alloy Nos. S41 to S45).
3)能夠確認藉由含有Bi,切削阻力進一步降低(合金No.S43)。 3) It was confirmed that by including Bi, the cutting resistance was further reduced (Alloy No. S43).
4)能夠確認藉由於κ相中含有0.08mass%以上的Sn、0.07mass%以上的P,從而提高耐蝕性、切削性能、強度(例如合金No.S01、S02、S13)。 4) It can be confirmed that the κ phase contains 0.08 mass% or more of Sn and 0.07 mass% or more of P, thereby improving corrosion resistance, cutting performance, and strength (for example, alloy Nos. S01, S02, and S13).
5)能夠確認藉由於α相中存在細長的針狀κ相亦即κ1相,從而強度上升,強度指數提高,切削性得到良好地保持,耐蝕性提高(例如合金No.S01、S02、13)。 5) It can be confirmed that due to the presence of the slender needle-like κ phase, that is, the κ1 phase, in the α phase, the strength is increased, the strength index is improved, the machinability is well maintained, and the corrosion resistance is improved (for example, alloy Nos. S01, S02, 13) .
6)若Cu含量少,則γ相增加,切削性良好,但耐蝕性、衝擊特性、高溫特性變差。相反,若Cu含量多,則切削性變差。又,衝擊特性亦變差(合金No.S119、S120、S122等)。 6) When the Cu content is small, the γ phase increases and the machinability is good, but the corrosion resistance, impact characteristics, and high-temperature characteristics deteriorate. Conversely, when the Cu content is large, the machinability is deteriorated. In addition, the impact characteristics are also deteriorated (Alloy Nos. S119, S120, S122, etc.).
7)若Sn含量大於0.28mass%,則γ相的面積率將大於1.5%,切削性良好,但耐蝕性、衝擊特性、高溫特性變差(合金S111)。另一方面,若Sn含量小於0.07mass%,則惡劣的環境下的脫鋅腐蝕深度大(合金No.S114~S117)。若Sn含量為0.1mass%以上,則特性進一步改善(合金S26、S27、S28)。 7) If the Sn content is greater than 0.28 mass%, the area ratio of the γ phase will be greater than 1.5%, and the machinability is good, but the corrosion resistance, impact characteristics, and high temperature characteristics are deteriorated (Alloy S111). On the other hand, if the Sn content is less than 0.07 mass%, the depth of dezincification corrosion in a severe environment is large (Alloy Nos. S114 to S117). When the Sn content is 0.1 mass% or more, the characteristics are further improved (alloys S26, S27, and S28).
8)若P含量多,則衝擊特性變差。又,切削阻力略高。另一方面,若P含量少,則惡劣的環境下的脫鋅腐蝕深度大(合金No.S109、S113、S115)。 8) If the P content is large, the impact characteristics are deteriorated. The cutting resistance is slightly higher. On the other hand, if the P content is small, the depth of dezincification corrosion in a severe environment is large (Alloy Nos. S109, S113, and S115).
9)能夠確認即使含有可藉由實際操作進行之程度的不 可避免的雜質,亦不會較大影響各種特性(合金No.S01、S02、S03)。認為若含有係本實施形態的組成範圍外或者係邊界值的組成,但超過不可避免的雜質的限度之Fe,則形成Fe與Si的金屬間化合物、或Fe與P的金屬間化合物。 其結果,有效作用之Si濃度、P濃度減少,耐蝕性變差,與金屬間化合物的形成相互作用而切削性能略降低(合金No.S124、S125)。 9) It is possible to confirm that Avoidable impurities will not greatly affect various characteristics (Alloy Nos. S01, S02, S03). It is considered that if the composition is outside the composition range or the boundary value of the present embodiment, but exceeds the limit of unavoidable impurities, an intermetallic compound of Fe and Si or an intermetallic compound of Fe and P is formed. As a result, the effective Si concentration and P concentration are reduced, the corrosion resistance is deteriorated, and the interaction with the formation of the intermetallic compound reduces the cutting performance slightly (Alloy Nos. S124, S125).
10)若組成關係式f1的值低,則即使Cu、Si、Sn、P在組成範圍內,惡劣的環境下的脫鋅腐蝕深度亦較大(合金No.S110、S101、S126)。 10) If the value of the composition relational expression f1 is low, even if Cu, Si, Sn, and P are in the composition range, the depth of dezincification corrosion in a severe environment is large (Alloy Nos. S110, S101, and S126).
11)若組成關係式f1的值低,則γ相增加,切削性良好,但耐蝕性、衝擊特性、高溫特性變差。若組成關係式f1的值高,則κ相增加,切削性、熱加工性、衝擊特性變差(合金No.S109、S104、S125、S121)。 11) When the value of the composition relational expression f1 is low, the γ phase is increased and the machinability is good, but the corrosion resistance, impact characteristics, and high temperature characteristics are deteriorated. When the value of the composition relational expression f1 is high, the κ phase is increased, and the machinability, hot workability, and impact characteristics are deteriorated (Alloy Nos. S109, S104, S125, and S121).
12)若組成關係式f2的值低,則切削性良好,但熱加工性、耐蝕性、衝擊特性、高溫特性變差。若組成關係式f2的值高,則熱加工性變差,在熱擠壓中產生問題。又,切削性變差(合金No.S104、S105、S103、S118、S119、S120、S123)。 12) If the value of the composition relationship f2 is low, the machinability is good, but the hot workability, corrosion resistance, impact characteristics, and high temperature characteristics are deteriorated. When the value of the composition relational expression f2 is high, the hot workability is deteriorated, and a problem occurs in hot extrusion. In addition, the machinability deteriorated (Alloy Nos. S104, S105, S103, S118, S119, S120, S123).
13)在金相組織中,若γ相的比例大於1.5%或γ相的長邊的長度大於40μm,則切削性良好,但耐蝕性、衝擊特性、高溫特性變差。尤其,若γ相增加,則在惡劣的 環境下的脫鋅腐蝕試驗中產生γ相的選擇腐蝕(合金No.S101、S110、S126)。若γ相的比例為0.8%以下且γ相的長邊的長度為30μm以下,則耐蝕性、衝擊特性、高溫特性變得良好(合金No.S01、S11)。 13) In the metallographic structure, if the proportion of the γ phase is greater than 1.5% or the length of the long side of the γ phase is greater than 40 μm, the machinability is good, but the corrosion resistance, impact characteristics, and high temperature characteristics are deteriorated. In particular, if the γ phase increases, Selective corrosion of γ phase occurred in the dezincification corrosion test under the environment (alloy Nos. S101, S110, S126). When the ratio of the γ phase is 0.8% or less and the length of the long side of the γ phase is 30 μm or less, the corrosion resistance, impact characteristics, and high-temperature characteristics become good (Alloy Nos. S01 and S11).
若μ相的面積率大於2%或μ相的長邊的長度超過25μm,則耐蝕性、衝擊特性、高溫特性變差。在惡劣的環境下的脫鋅腐蝕試驗中產生晶界腐蝕或μ相的選擇腐蝕(合金No.S01,製程No.AH4、BH3、DH2)。若μ相的比例為1%以下且μ相的長邊的長度為15μm以下,則耐蝕性、衝擊特性、高溫特性變得良好(合金S01、S11)。 When the area ratio of the μ phase is more than 2% or the length of the long side of the μ phase exceeds 25 μm, the corrosion resistance, impact characteristics, and high-temperature characteristics are deteriorated. In the dezincification corrosion test under severe environment, grain boundary corrosion or μ-phase selective corrosion occurs (Alloy No. S01, Process No. AH4, BH3, DH2). When the proportion of the μ phase is 1% or less and the length of the long side of the μ phase is 15 μm or less, the corrosion resistance, impact characteristics, and high-temperature characteristics become good (alloys S01 and S11).
若κ相的面積率大於65%,則切削性、衝擊特性變差。 另一方面,若κ相的面積率小於25%,則切削性差(合金No.S122、S105)。 When the area ratio of the κ phase is more than 65%, the machinability and impact characteristics are deteriorated. On the other hand, if the area ratio of the κ phase is less than 25%, the machinability is poor (Alloy Nos. S122 and S105).
14)若組織關係式f5=(γ)+(μ)超過2.5%或f3=(α)+(κ)小於97%,則耐蝕性、衝擊特性、高溫特性變差。若組織關係式f5為1.5%以下,則耐蝕性、衝擊特性、高溫特性有所改善(合金No.S1,製程No.AH2、A1、合金No.S103、S23)。 14) If the structural relationship f5 = (γ) + (μ) exceeds 2.5% or f3 = (α) + (κ) is less than 97%, the corrosion resistance, impact characteristics, and high-temperature characteristics deteriorate. When the structural relational expression f5 is 1.5% or less, the corrosion resistance, impact characteristics, and high temperature characteristics are improved (Alloy No. S1, Process No. AH2, A1, Alloy No. S103, S23).
若組織關係式f6=(κ)+6×(γ)1/2+0.5×(μ)大於70或小於27,則切削性差(合金No.S105、122,製程No.E1、F1)。若f6為32以上且62以下,則切削性進一步提高(合金S01、S11)。 If the structural relationship formula f6 = (κ) + 6 × (γ) 1/2 + 0.5 × (μ) is greater than 70 or less than 27, the machinability is poor (Alloy Nos. S105 and 122, Process Nos. E1 and F1). When f6 is 32 or more and 62 or less, the machinability is further improved (alloys S01 and S11).
當γ相的面積率超過1.5%時,與組織關係式f6的值無關地,切削阻力降低,切屑的形狀亦存在較多良好者(合金No.S103、S112等)。 When the area ratio of the γ phase exceeds 1.5%, irrespective of the value of the structural relationship f6, the cutting resistance is reduced and the shape of the chip is also good (alloys S103, S112, etc.).
15)若κ相中所含之Sn量低於0.08mass%,則惡劣的環境下的脫鋅腐蝕深度增大,會產生κ相的腐蝕。又,切削阻力亦略高,亦存在切屑的分割性差者(合金No.S114~S117)。若κ相中所含之Sn量大於0.11mass%,則耐蝕性、切削性變得良好(合金S26、S27、S28)。 15) If the amount of Sn contained in the κ phase is less than 0.08 mass%, the depth of dezincification corrosion in a severe environment will increase, and corrosion of the κ phase will occur. In addition, the cutting resistance was also slightly higher, and there were also cases where the chip had poor segmentability (Alloy Nos. S114 to S117). When the amount of Sn contained in the κ phase is more than 0.11 mass%, the corrosion resistance and the machinability become good (alloys S26, S27, and S28).
16)若κ相中所含之P量低於0.07mass%,則惡劣的環境下的脫鋅腐蝕深度增大,會產生κ相的腐蝕。(合金No.S113、S115、S116)。 16) If the amount of P contained in the κ phase is less than 0.07 mass%, the depth of dezincification corrosion in a severe environment will increase, and corrosion of the κ phase will occur. (Alloy Nos. S113, S115, S116).
17)若γ相的面積率為1.5%以下,則κ相中所含之Sn濃度及P濃度高於合金中所含之Sn的量及P的量。與合金中所含之Sn的量及P的量相比,γ相的面積率變得越小,κ相中所含之Sn濃度及P濃度則進一步提高。相反,若γ相的面積率大,則κ相中所含之Sn濃度低於合金中所含之Sn的量。尤其,若γ相的面積率約成為10%,則κ相中所含之Sn濃度約成為合金中所含之Sn的量的一半(合金S01、S02、S03、S14、S101、S108)。又,例如在合金S20中,若γ相的面積率從5.9%減小至0.5%,則α相的Sn濃度從0.13mass%至0.18mass%增加0.05mass%,κ相的Sn濃度從0.22mass%至0.31mass%增加0.09mass%。這樣,κ相的Sn 的增加量超過α相的Sn的增加量。若γ相的減少,則藉由Sn在κ相中分佈的增加及α相中存在較多針狀κ相,切削阻力增加7N,但維持良好的切削性,藉由增強κ相的耐蝕性,脫鋅腐蝕深度減少為約1/4,衝擊值約成為1/2,高溫潛變減少為1/3,抗拉強度提高43N/mm2,強度指數增加了77。 17) If the area ratio of the γ phase is 1.5% or less, the Sn and P concentrations contained in the κ phase are higher than the amounts of Sn and P contained in the alloy. Compared with the amount of Sn and P contained in the alloy, the smaller the area ratio of the γ phase, the higher the Sn concentration and the P concentration contained in the κ phase. On the contrary, if the area ratio of the γ phase is large, the concentration of Sn contained in the κ phase is lower than the amount of Sn contained in the alloy. In particular, if the area ratio of the γ phase is approximately 10%, the Sn concentration contained in the κ phase is approximately half of the amount of Sn contained in the alloy (alloys S01, S02, S03, S14, S101, S108). For example, in alloy S20, if the area ratio of the γ phase is reduced from 5.9% to 0.5%, the Sn concentration of the α phase increases from 0.13 mass% to 0.18 mass% by 0.05 mass%, and the Sn concentration of the κ phase increases from 0.22 mass. % To 0.31mass% increased by 0.09mass%. Thus, the increase amount of Sn in the κ phase exceeds the increase amount of Sn in the α phase. If the γ phase decreases, the increase in the distribution of Sn in the κ phase and the presence of more needle-like κ phases in the α phase will increase the cutting resistance by 7N, but maintain good machinability and enhance the corrosion resistance of the κ phase. Dezincification corrosion depth is reduced to approximately 1/4, impact value is approximately 1/2, high temperature creep is reduced to 1/3, tensile strength is increased by 43N / mm 2 , and strength index is increased by 77.
18)只要滿足全部組成的要件、金相組織的要件,則抗拉強度為530N/mm2以上,負載相當於室溫下的0.2%保證應力之荷載並於50℃保持100小時時的潛變應變為0.3%以下(合金No.S103、S112等)。 18) As long as the requirements for all components and metallographic structure are met, the tensile strength is 530 N / mm 2 or more, the load is equivalent to 0.2% of the guaranteed stress at room temperature and the creep is maintained at 50 ° C for 100 hours. The strain is 0.3% or less (alloy Nos. S103, S112, etc.).
19)只要滿足全部組成的要件、金相組織的要件,則U形凹口的夏比衝擊試驗值為14J/cm2以上。在未實施冷加工的熱擠出材料或鍛造材料中,U形凹口的夏比衝擊試驗值為17J/cm2以上。而且,強度指數亦超過670(合金No.S01、S02、S13、S14等)。 19) As long as the requirements for the entire composition and the requirements for the metallographic structure are satisfied, the Charpy impact test value of the U-shaped notch is 14 J / cm 2 or more. The Charpy impact test value of the U-shaped notch in a hot-extruded material or a forged material that has not been cold-worked is 17 J / cm 2 or more. Moreover, the strength index also exceeded 670 (alloy Nos. S01, S02, S13, S14, etc.).
Si量約為2.95%,於α相內開始存在針狀κ相,Si量約為3.1%,針狀κ相大幅增加。關係式f2影響了針狀κ相的量(合金No.S31、S32、S101、S107、S108等)。 The amount of Si was about 2.95%, and the needle-like κ phase began to exist in the α phase. The amount of Si was about 3.1%, and the needle-like κ phase increased significantly. The relationship f2 affects the amount of acicular κ phase (alloy Nos. S31, S32, S101, S107, S108, etc.).
若針狀κ相的量增加,則切削性、抗拉強度、高溫特性變得良好。推測為關係到α相的增強、切屑分割性(合金No.S02、S13、S23、S31、S32、S101、S107、S108等)。 When the amount of the acicular κ phase increases, the machinability, tensile strength, and high-temperature characteristics become good. It is presumed to be related to the enhancement of the α phase and chip splitting properties (alloy Nos. S02, S13, S23, S31, S32, S101, S107, S108, etc.).
ISO6509的試驗方法中,含有約3%以上的β相或約5% 以上的γ相,或者不含P或含有0.01%之合金為不合格(評價:△、×),但含有3~5%的γ相且含有約3%的μ相之合金為合格(評價:○)。本實施形態中所採用之腐蝕環境係基於假設了惡劣環境者(合金No.S14、S106、S107、S112、S120)。 The test method of ISO6509 contains more than 3% β phase or about 5% The above γ phase, or alloys containing no P or 0.01% are unacceptable (evaluation: △, ×), but alloys containing 3 to 5% γ phase and approximately 3% of the mu phase are acceptable (evaluation: ○). The corrosive environment used in this embodiment is based on those who assume a harsh environment (Alloy Nos. S14, S106, S107, S112, S120).
就耐磨耗性而言,存在許多針狀κ相且含有約0.10%~0.25%的Sn、含有約0.1~約1.0%的γ相之合金,無論在潤滑下還是在無潤滑下均優異(合金No.S14、S18等)。 In terms of wear resistance, an alloy having many needle-like kappa phases, containing about 0.10% to 0.25% of Sn, and containing about 0.1 to about 1.0% of the γ phase, is excellent both under lubrication and without lubrication ( Alloy No. S14, S18, etc.).
20)使用了量產設備之材料和在實驗室中製成之材料的評價中,得到了大致相同的結果(合金No.S01、S02,製程No.C1、C2、E1、F1)。 20) Evaluation of materials using mass production equipment and materials made in the laboratory yielded approximately the same results (Alloy No. S01, S02, Process No. C1, C2, E1, F1).
21)關於製造條件: 若針對熱擠出材料、擠壓/拉伸之材料、熱鍛造品,在510℃以上且575℃以上的溫度區域內保持20分鐘以上,或者在連續爐中,在510℃以上且575℃以上的溫度,以2.5℃/分鐘以下的平均冷卻速度進行冷卻,並且在480℃至370℃的溫度區域以2.5℃/分鐘以上的平均冷卻速度進行冷卻,則得到γ相大幅減少、幾乎不存在μ相,且耐蝕性、高溫特性、衝擊特性、機械強度優異之材料。 21) About manufacturing conditions: For hot-extruded materials, extruded / stretched materials, and hot-forged products, hold for more than 20 minutes in a temperature range of 510 ° C and above 575 ° C or in a continuous furnace at 510 ° C and above 575 ° C When the temperature is cooled at an average cooling rate of 2.5 ° C / min or less, and at an average cooling rate of 2.5 ° C / min or more in a temperature range of 480 ° C to 370 ° C, the γ phase is greatly reduced and there is almost no μ Materials with excellent corrosion resistance, high temperature characteristics, impact characteristics, and mechanical strength.
在對熱加工材料及冷加工材料進行熱處理之製程中,若熱處理的溫度低,則γ相的減少較少,耐蝕性、衝擊特性、高溫特性差。若熱處理的溫度高,則α相的晶粒變得 粗大,γ相的減少較少,因此耐蝕性、衝擊特性差,切削性亦差,抗拉強度亦低(合金No.S01、S02、S03,製程No.A1、AH5、AH6)。又,當熱處理的溫度為520℃時,若保持時間短,則γ相的減少較少。若將熱處理的時間(t)和熱處理的溫度(T)之間的關係表示於數式中,則為(T-500)×t(其中,T為540℃以上時,設為540),若該數式為800以上,則γ相減少得更多(製程No.A5、A6、D1、D4、F1)。 In the process of heat-treating hot-worked materials and cold-worked materials, if the temperature of the heat treatment is low, the reduction of the γ phase is small, and the corrosion resistance, impact characteristics, and high-temperature characteristics are poor. If the temperature of the heat treatment is high, the crystal grains of the α phase become Coarse, less reduction of γ phase, so poor corrosion resistance, impact characteristics, poor machinability, and low tensile strength (alloy No. S01, S02, S03, process No. A1, AH5, AH6). When the heat treatment temperature is 520 ° C., if the holding time is short, the decrease in the γ phase is small. If the relationship between the heat treatment time (t) and the heat treatment temperature (T) is expressed in the formula, it is (T-500) × t (where T is 540 ° C or higher, it is 540). When the formula is 800 or more, the γ phase decreases more (process Nos. A5, A6, D1, D4, and F1).
在熱處理後的冷卻中,若在470℃至380℃的溫度區域的平均冷卻速度慢,則存在μ相,耐蝕性、衝擊特性、高溫特性差,抗拉強度亦低(合金No.S01、S02、S03,製程No.A1~A4、AH8、DH2、DH3)。 In the cooling after heat treatment, if the average cooling rate in the temperature range of 470 ° C to 380 ° C is slow, there are μ phases, and the corrosion resistance, impact characteristics, and high temperature characteristics are poor, and the tensile strength is also low (Alloy Nos. S01, S02 , S03, process No. A1 ~ A4, AH8, DH2, DH3).
在熱處理後,熱擠出材料的溫度低的一方的γ相所佔之比例亦較少,耐蝕性、衝擊特性、抗拉強度、高溫特性良好。(合金No.S01、S02、S03,製程No.A1、A9) After the heat treatment, the proportion of the γ phase of the hot-extruded material is low, and the corrosion resistance, impact characteristics, tensile strength, and high-temperature characteristics are good. (Alloy No.S01, S02, S03, Process No.A1, A9)
作為熱處理方法,暫且將溫度提高至575℃~620℃,在冷卻過程中減緩在575℃至510℃的溫度區域的平均冷卻速度,藉此得到良好的耐蝕性、衝擊特性、高溫特性。 在連續熱處理方法中亦能夠確認到特性的改善(合金No.S01、S02、S03,製程No.A1、A7、A8、D5)。 As a heat treatment method, temporarily increase the temperature to 575 ° C to 620 ° C, and slow down the average cooling rate in the temperature region of 575 ° C to 510 ° C during the cooling process, thereby obtaining good corrosion resistance, impact characteristics, and high temperature characteristics. Improvements in characteristics were also confirmed in the continuous heat treatment method (alloy Nos. S01, S02, S03, process Nos. A1, A7, A8, D5).
在熱處理中,若將溫度提高至635℃,則γ相的長邊的長度變長,耐蝕性差、強度降低。即使於500℃進行長 時間的加熱保持,γ相的減少亦少(合金No.S01、S02、S03,製程No.AH5、AH6)。 In the heat treatment, if the temperature is increased to 635 ° C, the length of the long side of the γ phase becomes longer, the corrosion resistance is poor, and the strength is reduced. Even at 500 ° C The heating and holding time, the reduction of the γ phase is also small (alloy No. S01, S02, S03, process No. AH5, AH6).
在熱鍛造後的冷卻中,藉由將在575℃至510℃的溫度區域的平均冷卻速度控制為1.5℃/分鐘,得到熱鍛造後的γ相所佔之比例少的鍛造品。(合金No.S01、S02、S03,製程No.D6)。 In the cooling after hot forging, by controlling the average cooling rate in the temperature range of 575 ° C to 510 ° C to 1.5 ° C / min, a forged product having a small proportion of the γ phase after hot forging is obtained. (Alloy No. S01, S02, S03, Process No. D6).
即使使用連續鑄造棒作為熱鍛造原材料,亦與擠出材料相同地得到良好的各種特性(合金No.S01、S02、S03,製程No.F3、F4)。 Even if a continuous casting rod is used as a hot forging raw material, good various characteristics (alloy Nos. S01, S02, S03, and process Nos. F3, F4) are obtained similarly to the extruded material.
藉由適當的熱處理及熱鍛造後的適當的冷卻條件,增加了κ相中所含之Sn量、P量(合金No.S01、S02、S03,製程No.A1、AH1、C0、C1、D6)。 With proper heat treatment and appropriate cooling conditions after hot forging, the amount of Sn and P contained in the κ phase (alloy No. S01, S02, S03, process No. A1, AH1, C0, C1, D6 ).
若在對擠出材料實施了加工率為約5%、約9%的冷加工之後進行規定的熱處理,則與熱擠出材料相比,耐蝕性、衝擊特性、高溫特性、抗拉強度提高,尤其抗拉強度增加約70N/mm2、約90N/mm2,強度指數亦提高約90(合金No.S01、S02、S03,製程No.AH1、A1、A12)。藉由對冷加工材料在540℃的高溫下進行熱處理(退火),能夠得到維持良好的切削性,耐蝕性優異,高強度,且高溫特性、衝擊特性優異之合金。 After subjecting the extruded material to cold processing at a processing rate of about 5% and about 9%, a predetermined heat treatment is performed, and the corrosion resistance, impact characteristics, high temperature characteristics, and tensile strength of the extruded material are improved compared to hot extruded materials. The tensile strength is increased by about 70 N / mm 2 , about 90 N / mm 2 , and the strength index is also increased by about 90 (alloy No. S01, S02, S03, process No. AH1, A1, A12). By performing heat treatment (annealing) of the cold-worked material at a high temperature of 540 ° C, an alloy can be obtained which maintains good machinability, has excellent corrosion resistance, high strength, and has high temperature characteristics and impact characteristics.
若對熱處理材料以5%的冷加工率進行加工,則與擠出材料相比,抗拉強度增加約90N/mm2,衝擊值為同等以上, 耐蝕性、高溫特性亦有所提高。若將冷加工率設為約9%,則抗拉強度增加約140N/mm2,但衝擊值略有降低(合金No.S01、S02、S03,製程No.AH1、A10、A11)。 When the heat-treated material is processed at a cold working rate of 5%, the tensile strength is increased by about 90 N / mm 2 compared with the extruded material, and the impact value is the same or more, and the corrosion resistance and high temperature characteristics are also improved. When the cold working ratio is set to about 9%, the tensile strength is increased by about 140 N / mm 2 , but the impact value is slightly reduced (alloy Nos. S01, S02, and S03, process Nos. AH1, A10, and A11).
若對熱加工材料實施規定的熱處理,則確認到κ相中所含之Sn的量增加,γ相大幅減少,但能夠確保良好的切削性(合金No.S01、S02,製程No.AH1、A1、D7、C0、C1、EH1、E1、FH1、F1)。 When a predetermined heat treatment is performed on the hot-worked material, it is confirmed that the amount of Sn contained in the κ phase increases and the γ phase decreases significantly, but good machinability is ensured (Alloy Nos. S01 and S02, Process Nos. AH1, A1 , D7, C0, C1, EH1, E1, FH1, F1).
若實施適當的熱處理,則於α相中將存在針狀κ相(合金No.S01、S02、S03,製程No.AH1、A1、D7、C0、C1、EH1、E1、FH1、F1)。推測為藉由於α相中存在針狀κ相,抗拉強度、耐磨耗性得到提高,切削性亦良好,補償了γ相的大幅減少。 If an appropriate heat treatment is performed, acicular κ phases (alloy Nos. S01, S02, and S03, process Nos. AH1, A1, D7, C0, C1, EH1, E1, FH1, and F1) will be present in the α phase. It is presumed that due to the presence of the needle-like κ phase in the α phase, the tensile strength and abrasion resistance are improved, and the machinability is also good, which compensates for the substantial decrease in the γ phase.
能夠確認在冷加工後或熱加工後進行低溫退火的情況下,以240℃以上且350℃以下的溫度從10分鐘加熱至300分鐘,將加熱溫度設為T℃、將加熱時間設為t分鐘時,若以150(T-220)×(t)1/2 1200的條件進行熱處理,則能夠得到具備惡劣的環境下的優異之耐蝕性,帶有良好的衝擊特性、高溫特性之冷加工材料、熱加工材料(合金No.S01,製程No.B1~B3)。 When low temperature annealing is performed after cold working or hot working, it can be confirmed that heating is performed at a temperature of 240 ° C or higher and 350 ° C or lower from 10 minutes to 300 minutes, and the heating temperature is set to T ° C and the heating time is set to t minutes. If 150 (T-220) × (t) 1/2 If the heat treatment is performed under the conditions of 1200, a cold-worked material and a hot-worked material (alloy No. S01, process No. B1 to B3) having excellent corrosion resistance in a harsh environment, good impact characteristics, and high temperature characteristics can be obtained.
在對合金No.S01~S03實施了製程No.AH9之試樣中,由於變形阻力高,未能擠出至最後,因此中止了之後的評價。 In the samples in which alloys No. S01 to S03 were subjected to the process No. AH9, the deformation resistance was high and they could not be squeezed out to the end, so the subsequent evaluation was suspended.
在製程No.BH1中,矯正不充分且低溫退火不適當,從而產生品質上問題。 In the process No. BH1, inadequate correction and low temperature annealing are not appropriate, thereby causing quality problems.
依以上情況,如本實施形態的合金那樣,各添加元素的含量和各組成關係式、金相組織、各組織關係式在適當的範圍內之本實施形態的合金係熱加工性(熱擠壓、熱鍛造)優異,且耐蝕性、切削性亦良好。又,為了在本實施形態的合金中獲得優異之特性,能夠藉由將熱擠壓及熱鍛造中的製造條件、熱處理中的條件設為適當範圍來實現。 According to the above, as in the alloy of the present embodiment, the alloy system of the present embodiment has a hot workability (hot extrusion) in which the content of each additional element, the composition relationship formula, the metallographic structure, and the structure relationship formula are within appropriate ranges. , Hot forging) is excellent, and corrosion resistance and machinability are also good. In addition, in order to obtain excellent characteristics in the alloy of this embodiment, it can be achieved by setting the manufacturing conditions during hot extrusion and hot forging, and the conditions during heat treatment to appropriate ranges.
(實施例2) (Example 2)
關於本實施形態的比較例之合金,得到了在惡劣的水環境下使用了8年之銅合金Cu-Zn-Si合金鑄件(試驗No.T601/合金No.S201)。再者,並沒有所使用之環境的水質等詳細資料。藉由與實施例1相同的方法進行了試驗No.T601的組成、金相組織的分析。又,使用金屬顯微鏡對截面的腐蝕狀態進行了觀察。詳細而言,以使曝露表面與長邊方向保持垂直之方式,將試樣植入酚醛樹脂材料中。 接著,以使腐蝕部的截面作為最長的切斷部而獲得之方式切斷了試樣。接著對試樣進行了研磨。使用金屬顯微鏡對截面進行了觀察。又測定了最大腐蝕深度。 As for the alloy of the comparative example of this embodiment, a copper alloy Cu-Zn-Si alloy casting (test No. T601 / alloy No. S201) which had been used for 8 years in a severe water environment was obtained. Furthermore, there is no detailed information on the water quality of the environment used. The composition and metallographic analysis of Test No. T601 were performed in the same manner as in Example 1. Moreover, the corrosion state of the cross section was observed using a metal microscope. Specifically, the sample was implanted into the phenol resin material so that the exposed surface was perpendicular to the long side direction. Next, the sample was cut so that the cross section of the corroded part was obtained as the longest cut part. The sample was then ground. The cross section was observed using a metal microscope. The maximum corrosion depth was measured.
接著,在與試驗No.T601相同的組成及製作條件下製作出類似的合金鑄件(試驗No.T602/合金No.S202)。對於類似的合金鑄件(試驗No.T602),進行了實施例1中記載 的組成、金相組織的分析、機械特性等的評價(測定)及脫鋅腐蝕試驗1~3。而且,對試驗No.T601的基於實際的水環境之腐蝕狀態與試驗No.T602的脫鋅腐蝕試驗1~3的基於加速試驗之腐蝕狀態進行比較,驗證脫鋅腐蝕試驗1~3的加速試驗的有效性。 Next, a similar alloy casting was produced under the same composition and production conditions as those of Test No. T601 (Test No. T602 / Alloy No. S202). A similar alloy casting (Test No. T602) was described in Example 1. Composition, analysis of metallographic structure, evaluation (measurement) of mechanical properties, etc., and dezincification corrosion tests 1 to 3. Furthermore, the corrosion state based on the actual water environment of test No. T601 and the corrosion state based on the accelerated test of dezincification corrosion tests 1 to 3 of test No. T602 were compared to verify the accelerated test of the dezincification corrosion tests 1 to 3 Effectiveness.
又,對實施例1中記載的本實施形態的合金(試驗No.T28/合金No.S01/製程No.C2)的脫鋅腐蝕試驗1的評價結果(腐蝕狀態)與試驗No.T601的腐蝕狀態和試驗No.T602的脫鋅腐蝕試驗1的評價結果(腐蝕狀態)進行比較,考察了試驗No.T28的耐蝕性。 In addition, the evaluation results (corrosion state) of the dezincification corrosion test 1 of the alloy (Test No. T28 / Alloy No. S01 / Process No. C2) of this embodiment described in Example 1 and the corrosion of Test No. T601 The state and the evaluation result (corrosion state) of the dezincification corrosion test 1 of Test No. T602 were compared, and the corrosion resistance of Test No. T28 was examined.
藉由以下方法製作出試驗No.T602。 Test No. T602 was produced by the following method.
以成為與試驗No.T601(合金No.S201)大致相同組成之方式熔解原料,於澆鑄溫度1000℃澆鑄於內徑φ40mm的鑄模中,從而製作出鑄件。之後,關於鑄件,在575℃~510℃的溫度區域以約20℃/分鐘的平均冷卻速度進行冷卻,繼而,在470℃至380℃的溫度區域以約15℃/分鐘的平均冷卻速度進行冷卻。藉由上述,製作出試驗No.T602的試樣。 The raw materials were melted so as to have a composition almost the same as that of Test No. T601 (Alloy No. S201), and were cast into a mold having an inner diameter of φ40 mm at a casting temperature of 1000 ° C to produce a casting. After that, the casting is cooled at a temperature range of 575 ° C to 510 ° C at an average cooling rate of about 20 ° C / min, and then at a temperature range of 470 ° C to 380 ° C at an average cooling rate of about 15 ° C / min. . Based on the above, a sample of Test No. T602 was produced.
組成、金相組織的分析方法、機械特性等的測定方法及脫鋅腐蝕試驗1~3的方法如實施例1中所記載。 The composition, the analysis method of the metallographic structure, the measurement methods of the mechanical properties, and the methods of the dezincification corrosion tests 1 to 3 are as described in Example 1.
將所得之結果示於表48~表50及圖4。 The obtained results are shown in Tables 48 to 50 and FIG. 4.
在惡劣的水環境下使用了8年之銅合金鑄件(試驗No.T601)中,至少Sn、P的含量在本實施形態的範圍之外。 In a copper alloy casting (test No. T601) that has been used for 8 years in a harsh water environment, at least the contents of Sn and P are outside the range of this embodiment.
圖4(a)表示試驗No.T601的截面的金屬顯微照片。 FIG. 4 (a) shows a metal micrograph of a cross section of Test No. T601.
試驗No.T601中,在惡劣的水環境下使用了8年,因該使用環境而產生之腐蝕的最大腐蝕深度為138μm。 In Test No. T601, after 8 years of use in a harsh water environment, the maximum corrosion depth of the corrosion caused by the use environment was 138 μm.
在腐蝕部的表面,與α相、κ相無關地產生了脫鋅腐蝕(自表面起平均約100μm的深度)。 Dezincification corrosion (a depth of about 100 μm from the surface on the average) occurred on the surface of the corroded part regardless of the α phase and the κ phase.
在α相、κ相被腐蝕之腐蝕部分中,隨著朝向內部而存在無疵α相。 In the corroded portion where the α phase and the κ phase are corroded, there is a non-defective α phase as it goes toward the inside.
α相、κ相的腐蝕深度具有凹凸而非恆定,大致從其邊界部朝向內部,腐蝕僅產生於γ相(從α相、κ相被腐蝕之邊界部分朝向內部約40μm的深度:局部產生之僅γ相上的腐蝕)。 The corrosion depth of the α phase and κ phase has unevenness rather than constant. It is generally from the boundary to the inside. Corrosion occurs only in the γ phase (from the boundary portion where the α and κ phases are corroded to a depth of about 40 μm: locally generated. Corrosion on the γ phase only).
圖4(b)表示試驗No.T602的脫鋅腐蝕試驗1之後的截面的金屬顯微照片。 FIG. 4 (b) shows a metal micrograph of a cross section after the dezincification corrosion test 1 of Test No. T602.
最大腐蝕深度為146μm。 The maximum corrosion depth is 146 μm.
在腐蝕部的表面,與α相、κ相無關地產生了脫鋅腐蝕(自表面起平均約100μm的深度)。 Dezincification corrosion (a depth of about 100 μm from the surface on the average) occurred on the surface of the corroded part regardless of the α phase and the κ phase.
其中,隨著朝向內部而存在無疵α相。 Among them, there is a non-defective α phase as it goes toward the inside.
α相、κ相的腐蝕深度具有凹凸而非恆定,大致從其邊界部朝向內部,腐蝕僅產生於γ相(從α相、κ相被腐蝕之邊界部分,只有局部產生之γ相的腐蝕長度約為45μm)。 The corrosion depth of the α phase and κ phase is uneven and not constant, and generally from the boundary portion toward the inside. Corrosion occurs only in the γ phase (from the boundary portion where the α phase and κ phase are corroded, only the locally generated γ phase corrosion length (Approximately 45 μm).
得知圖4(a)的在8年間由於惡劣的水環境產生之腐蝕與圖4(b)的藉由脫鋅腐蝕試驗1產生之腐蝕為大致相同的腐蝕形態。又,Sn、P的量不滿足本實施形態的範圍,因此在水與試驗液接觸之部分,α相和κ相這兩者腐蝕,在腐蝕部的末端,γ相在各處選擇性腐蝕。再者,κ相中的Sn及P的濃度低。 It is understood that the corrosion caused by the awful water environment in FIG. 4 (a) during 8 years is substantially the same as the corrosion generated by the dezincification corrosion test 1 in FIG. 4 (b). In addition, since the amounts of Sn and P do not satisfy the range of the present embodiment, both the α phase and the κ phase are corroded at the portion where water is in contact with the test solution, and the γ phase is selectively corroded at the ends of the corroded portion. The concentrations of Sn and P in the κ phase are low.
試驗No.T601的最大腐蝕深度略淺於試驗No.T602的脫鋅腐蝕試驗1中的最大腐蝕深度。但是,試驗No.T601的最大腐蝕深度略深於試驗No.T602的脫鋅腐蝕試驗2中的最大腐蝕深度。由實際的水環境引起之腐蝕的程度受到水質的影響,但脫鋅腐蝕試驗1、2的結果與由實際的水環境引起之腐蝕結果在腐蝕形態和腐蝕深度這兩者中大致一致。因此,得知脫鋅腐蝕試驗1、2的條件係有效,在脫鋅腐蝕試驗1、2中,得到與由實際的水環境引起之腐蝕結果大致相同的評價結果。 The maximum corrosion depth of test No. T601 is slightly shallower than the maximum corrosion depth of dezincification corrosion test 1 of test No. T602. However, the maximum corrosion depth of Test No. T601 is slightly deeper than the maximum corrosion depth of Dezincification Corrosion Test 2 of Test No. T602. The degree of corrosion caused by the actual water environment is affected by the water quality, but the results of the dezincification corrosion test 1 and 2 and the corrosion result by the actual water environment are roughly consistent in both the corrosion form and the corrosion depth. Therefore, it was found that the conditions of the dezincification corrosion tests 1 and 2 are valid, and in the dezincification corrosion tests 1 and 2, evaluation results that are substantially the same as the corrosion results caused by the actual water environment were obtained.
又,腐蝕試驗方法1、2的加速試驗的加速率與由實際惡劣的水環境引起之腐蝕大致一致,認為該情況基於腐蝕試驗方法1、2係假設了惡劣環境者。 The acceleration rate of the corrosion test methods 1 and 2 is approximately the same as the corrosion caused by the actual harsh water environment. It is considered that this case is based on the corrosion test methods 1 and 2 assuming severe environments.
試驗No.T602的脫鋅腐蝕試驗3(ISO6509脫鋅腐蝕試驗)的結果為“○”(good)。因此,脫鋅腐蝕試驗3的結果與由實際的水環境引起之腐蝕結果不一致。 The result of the dezincification corrosion test 3 (ISO6509 dezincification corrosion test) of Test No. T602 was "Good" (good). Therefore, the results of the dezincification corrosion test 3 do not agree with the corrosion results caused by the actual water environment.
脫鋅腐蝕試驗1的試驗時間為兩個月,約為75~100 倍的加速試驗。脫鋅腐蝕試驗2的試驗時間為三個月,約為30~50倍的加速試驗。相對於此,脫鋅腐蝕試驗3(ISO6509脫鋅腐蝕試驗)的試驗時間為24小時,約為1000倍以上的加速試驗。 The test time for dezincification corrosion test 1 is two months, about 75 ~ 100 Times the accelerated test. The test time of the dezincification corrosion test 2 is three months, which is about 30 to 50 times the accelerated test. On the other hand, the test time of the dezincification corrosion test 3 (ISO6509 dezincification corrosion test) is 24 hours, which is an accelerated test of about 1000 times or more.
如脫鋅腐蝕試驗1、2,認為藉由使用更接近實際的水環境之試驗液進行兩、三個月的長時間的試驗,從而得到與由實際的水環境引起之腐蝕結果大致相同的評價結果。 For example, the dezincification corrosion tests 1 and 2 are considered to be performed for a long period of two to three months by using a test liquid closer to the actual water environment, thereby obtaining an evaluation approximately the same as the corrosion results caused by the actual water environment. result.
尤其,在試驗No.T601的在8年間由惡劣的水環境引起之腐蝕結果和試驗No.T602的脫鋅腐蝕試驗1、2的腐蝕結果中,γ相與表面的α相、κ相的腐蝕一同被腐蝕。但是,在脫鋅腐蝕試驗3(ISO6509脫鋅腐蝕試驗)的腐蝕結果中,γ相幾乎未腐蝕。因此,認為在脫鋅腐蝕試驗3(ISO6509脫鋅腐蝕試驗)中,無法適當地評價與表面的α相、κ相的腐蝕一同進行的γ相的腐蝕,並且與由實際的水環境引起之腐蝕結果不一致。 In particular, in the corrosion results of test No. T601 caused by a severe water environment in 8 years and the corrosion results of dezincification corrosion tests 1 and 2 of test No. T602, the corrosion of the γ phase to the α phase and κ phase of the surface Corroded together. However, in the corrosion results of the dezincification corrosion test 3 (ISO6509 dezincification corrosion test), the γ phase was hardly corroded. Therefore, it is considered that in the dezincification corrosion test 3 (ISO6509 dezincification corrosion test), it is not possible to properly evaluate the corrosion of the γ phase with the corrosion of the α phase and the κ phase on the surface and the corrosion caused by the actual water environment The results were inconsistent.
圖4(c)表示試驗No.T28(合金No.S01/製程No.C2)的脫鋅腐蝕試驗1之後的截面的金屬顯微照片。 FIG. 4 (c) shows a metal micrograph of a cross section after the dezincification corrosion test 1 of Test No. T28 (Alloy No. S01 / Process No. C2).
在表面附近,露出於表面之γ相和κ相的約40%被腐蝕。但是,剩餘的κ相和α相無疵(未腐蝕)。腐蝕深度最大亦約為25μm。進而隨著朝向內部,以約20μm的深度產生了γ相或μ相的選擇性腐蝕。認為γ相或μ相的長邊的長度係確定腐蝕深度之很大因素之一。 Near the surface, about 40% of the γ and κ phases exposed on the surface are corroded. However, the remaining κ phase and α phase were flawless (uncorroded). The maximum corrosion depth is also about 25 μm. Furthermore, as it turned toward the inside, selective corrosion of a γ phase or a μ phase occurred at a depth of about 20 μm. It is considered that the length of the long side of the γ phase or the μ phase is one of the great factors determining the depth of corrosion.
與圖4(a)、(b)的試驗No.T601、T602相比,在圖4(c)的本實施形態的試驗No.T28中得知表面附近的α相及κ相的腐蝕大幅得到抑制。推測該情況延緩了腐蝕的進行。依腐蝕形態的觀察結果,作為表面附近的α相及κ相的腐蝕大幅得到抑制之主要因素,認為藉由使κ相含有Sn而提高了κ相的耐蝕性。 Compared with test Nos. T601 and T602 of FIGS. 4 (a) and (b), it was found in test No. T28 of this embodiment of FIG. 4 (c) that the corrosion of the α phase and the κ phase near the surface was greatly obtained. inhibition. It is presumed that this delays the progress of corrosion. According to the observation results of the corrosion morphology, it is considered that the corrosion resistance of the κ phase is improved by including Sn in the κ phase as a main factor that greatly suppresses the corrosion of the α phase and the κ phase near the surface.
本發明的易削性銅合金的熱加工性(熱擠壓性及熱鍛造性)優異,且耐蝕性、切削性優異。因此,本發明的易削性銅合金係適合於水龍頭、閥、接頭等在人和動物每日攝取之飲用水中使用之器具、閥、接頭、閥等電氣/汽車/機械/工業用配管構件、與液體接觸之器具、組件中。 The free-cutting copper alloy of the present invention is excellent in hot workability (hot-extrudability and hot-forgeability), and has excellent corrosion resistance and machinability. Therefore, the free-cutting copper alloy of the present invention is suitable for electrical / automotive / mechanical / industrial piping components such as faucets, valves, joints, and other appliances, valves, joints, and valves used in daily drinking water for humans and animals. In appliances and components in contact with liquid.
具體而言,能夠適當地適用為飲用水、排水、工業用水所流動之水龍頭配件、混合式水龍頭配件、排水配件、水龍頭本體、供熱水機組件、熱水器(EcoCute)組件、軟管配件、噴水器、水表、活栓、消防栓、軟管接頭、供排水旋塞(cock)、泵、集流管(header)、減壓閥、閥座、閘閥、閥、閥桿、管套節(union)、法蘭、分水旋塞(corporation cock)、水龍頭閥、球閥、各種閥、配管接頭的構成材料等,例如以彎管、插座、平筒(cheese)、彎頭、連接器、配接器、T形管、接頭(joint)等名稱使用者。 Specifically, it can be suitably applied to faucet fittings, mixed faucet fittings, drainage fittings, faucet bodies, hot water heater components, water heater (EcoCute) components, hose accessories, and water jets that are used for drinking water, drainage, and industrial water. Devices, water meters, hydrants, fire hydrants, hose connections, water supply and drainage cocks, pumps, headers, pressure reducing valves, valve seats, gate valves, valves, stems, unions, Flange, corporation cock, faucet valve, ball valve, various valves, piping joint materials, etc., such as elbow, socket, cheese, elbow, connector, adapter, T Tube, joints (joint) and other name users.
又,能夠適當地適用於作為汽車組件使用之電磁閥、 控制閥、各種閥、散熱器組件、油冷卻器組件、氣缸,作為機械用構件之配管接頭、閥、閥、閥桿、熱交換器組件、供排水旋塞、氣缸、泵,作為工業用配管構件之配管接頭、閥、閥、閥桿等中。 In addition, it can be suitably applied to a solenoid valve used as an automobile component, Control valves, various valves, radiator components, oil cooler components, cylinders, piping joints for mechanical components, valves, valves, stems, heat exchanger components, water supply and drainage cocks, cylinders, pumps, as industrial piping components Pipe fittings, valves, valves, stems, etc.
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Publication number | Priority date | Publication date | Assignee | Title |
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WO2018034284A1 (en) | 2016-08-15 | 2018-02-22 | 三菱伸銅株式会社 | Free-cutting copper alloy, and method for producing free-cutting copper alloy |
US11155909B2 (en) | 2017-08-15 | 2021-10-26 | Mitsubishi Materials Corporation | High-strength free-cutting copper alloy and method for producing high-strength free-cutting copper alloy |
KR102623143B1 (en) | 2019-06-25 | 2024-01-09 | 미쓰비시 마테리알 가부시키가이샤 | Free-cutting copper alloy castings, and method for manufacturing free-cutting copper alloy castings |
TWI731506B (en) | 2019-06-25 | 2021-06-21 | 日商三菱伸銅股份有限公司 | Free-cutting copper alloy and manufacturing method of free-cutting copper alloy |
KR20220059528A (en) | 2019-12-11 | 2022-05-10 | 미쓰비시 마테리알 가부시키가이샤 | A free-machining copper alloy, and a manufacturing method of a free-machining copper alloy |
KR102334814B1 (en) * | 2021-05-14 | 2021-12-06 | 주식회사 풍산 | Lead-free brass alloy for casting that does not contain lead and bismuth, and method for manufacturing the same |
CZ310004B6 (en) | 2021-09-22 | 2024-05-01 | CB21 Pharma, s.r.o | A formulation of cannabinoids for oral administration |
CN115354188B (en) * | 2022-08-26 | 2023-09-15 | 宁波金田铜业(集团)股份有限公司 | Easily-welded brass and preparation method thereof |
Citations (3)
Publication number | Priority date | Publication date | Assignee | Title |
---|---|---|---|---|
KR20070021137A (en) * | 2004-08-10 | 2007-02-22 | 삼보신도고교 가부기키가이샤 | Copper alloy |
WO2007043101A1 (en) * | 2005-09-30 | 2007-04-19 | Sanbo Shindo Kogyo Kabushiki Kaisha | Melted-solidified matter, copper alloy material for melting-solidification, and process for producing the same |
CN101098976A (en) * | 2005-09-22 | 2008-01-02 | 三宝伸铜工业株式会社 | Free-cutting copper alloy containing very low lead |
Family Cites Families (38)
Publication number | Priority date | Publication date | Assignee | Title |
---|---|---|---|---|
US4055445A (en) | 1974-09-20 | 1977-10-25 | Essex International, Inc. | Method for fabrication of brass alloy |
JPS63128142A (en) * | 1986-11-17 | 1988-05-31 | Nippon Mining Co Ltd | Free-cutting copper alloy |
US5288458A (en) * | 1991-03-01 | 1994-02-22 | Olin Corporation | Machinable copper alloys having reduced lead content |
US5865910A (en) | 1996-11-07 | 1999-02-02 | Waterbury Rolling Mills, Inc. | Copper alloy and process for obtaining same |
US7056396B2 (en) | 1998-10-09 | 2006-06-06 | Sambo Copper Alloy Co., Ltd. | Copper/zinc alloys having low levels of lead and good machinability |
US8506730B2 (en) * | 1998-10-09 | 2013-08-13 | Mitsubishi Shindoh Co., Ltd. | Copper/zinc alloys having low levels of lead and good machinability |
JP3917304B2 (en) * | 1998-10-09 | 2007-05-23 | 三宝伸銅工業株式会社 | Free-cutting copper alloy |
JP3734372B2 (en) | 1998-10-12 | 2006-01-11 | 三宝伸銅工業株式会社 | Lead-free free-cutting copper alloy |
JP2000119744A (en) * | 1998-10-16 | 2000-04-25 | Nkk Corp | Method for preventing hydrogen cracking at shearing time of high strength steel plate |
DE10308778B3 (en) | 2003-02-28 | 2004-08-12 | Wieland-Werke Ag | Lead-free brass with superior notch impact resistance, used in widely ranging applications to replace conventional brasses, has specified composition |
MY139524A (en) | 2004-06-30 | 2009-10-30 | Ciba Holding Inc | Stabilization of polyether polyol, polyester polyol or polyurethane compositions |
EP1777305B1 (en) | 2004-08-10 | 2010-09-22 | Mitsubishi Shindoh Co., Ltd. | Copper-base alloy casting with refined crystal grains |
KR100609357B1 (en) | 2004-08-17 | 2006-08-08 | 현대모비스 주식회사 | Axle inside depressing device with creeping speed in vehicle |
KR100662345B1 (en) | 2004-08-18 | 2007-01-02 | 엘지전자 주식회사 | A short message service control device for a mobile telecommunication terminal |
DE502005009545D1 (en) | 2004-10-11 | 2010-06-17 | Diehl Metall Stiftung & Co Kg | COPPER ZINC SILICON ALLOY, THEIR USE AND THEIR PREPARATION |
US7986112B2 (en) * | 2005-09-15 | 2011-07-26 | Mag Instrument, Inc. | Thermally self-stabilizing LED module |
US20070151064A1 (en) | 2006-01-03 | 2007-07-05 | O'connor Amanda L | Cleaning wipe comprising integral, shaped tab portions |
KR101133704B1 (en) | 2006-12-28 | 2012-04-06 | 가부시키가이샤 기츠 | Lead-free brass alloy with excellent resistance to stress corrosion cracking |
JP4266039B2 (en) | 2008-05-22 | 2009-05-20 | 京都ブラス株式会社 | Method for producing lead-free free-cutting brass alloy |
EP2634275B1 (en) * | 2010-10-25 | 2017-10-11 | Mitsubishi Shindoh Co., Ltd. | Pressure-resistant and corrosion-resistant copper alloy, brazed structure, and method for producing brazed structure |
KR20120057055A (en) | 2010-11-26 | 2012-06-05 | (주) 탐라그라스 | Smelting Furnace For Saving Energe |
WO2012169405A1 (en) * | 2011-06-06 | 2012-12-13 | 三菱マテリアル株式会社 | Copper alloy for electronic devices, method for producing copper alloy for electronic devices, copper alloy plastic working material for electronic devices, and component for electronic devices |
EP2757167B1 (en) * | 2011-09-16 | 2018-05-30 | Mitsubishi Shindoh Co., Ltd. | Copper alloy sheet and production method for copper alloy sheet |
TWI441932B (en) * | 2011-09-16 | 2014-06-21 | Mitsubishi Shindo Kk | Copper alloy plate and method for manufacturing copper alloy plate |
JP5386655B2 (en) * | 2011-09-20 | 2014-01-15 | 三菱伸銅株式会社 | Copper alloy plate and method for producing copper alloy plate |
CN103917674B (en) * | 2011-11-04 | 2015-06-03 | 三菱伸铜株式会社 | Hot-forged copper alloy article |
JP5763504B2 (en) * | 2011-11-11 | 2015-08-12 | 三菱伸銅株式会社 | Copper alloy rolling materials and rolled products |
AU2013340034B2 (en) * | 2012-10-31 | 2018-03-22 | Kitz Corporation | Brass alloy and processed part and wetted part |
CN103114220B (en) * | 2013-02-01 | 2015-01-21 | 路达(厦门)工业有限公司 | Excellent-thermoformability lead-free free-cutting corrosion-resistant brass alloy |
EP3050982B1 (en) * | 2013-09-26 | 2019-03-20 | Mitsubishi Shindoh Co., Ltd. | Copper alloy and copper alloy sheet |
CN105593390B (en) * | 2013-09-26 | 2017-03-22 | 三菱伸铜株式会社 | A copper alloy |
KR102370860B1 (en) * | 2014-03-25 | 2022-03-07 | 후루카와 덴키 고교 가부시키가이샤 | Copper alloy sheet material, connector, and method for manufacturing copper alloy sheet material |
CN106460135B (en) * | 2014-04-30 | 2018-05-15 | 株式会社开滋 | Product is soaked using the manufacture method and hot forging of the hot forging of brass and the valve, the fire hose that are shaped using the hot forging are first-class |
JP6558523B2 (en) | 2015-03-02 | 2019-08-14 | 株式会社飯田照明 | UV irradiation equipment |
CN105039777B (en) * | 2015-05-05 | 2018-04-24 | 宁波博威合金材料股份有限公司 | A kind of machinable brass alloys and preparation method |
US20170062615A1 (en) | 2015-08-27 | 2017-03-02 | United Microelectronics Corp. | Method of forming semiconductor device |
WO2019035224A1 (en) | 2017-08-15 | 2019-02-21 | 三菱伸銅株式会社 | Free-cutting copper alloy and method for producing free-cutting copper alloy |
WO2018034284A1 (en) * | 2016-08-15 | 2018-02-22 | 三菱伸銅株式会社 | Free-cutting copper alloy, and method for producing free-cutting copper alloy |
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Patent Citations (3)
Publication number | Priority date | Publication date | Assignee | Title |
---|---|---|---|---|
KR20070021137A (en) * | 2004-08-10 | 2007-02-22 | 삼보신도고교 가부기키가이샤 | Copper alloy |
CN101098976A (en) * | 2005-09-22 | 2008-01-02 | 三宝伸铜工业株式会社 | Free-cutting copper alloy containing very low lead |
WO2007043101A1 (en) * | 2005-09-30 | 2007-04-19 | Sanbo Shindo Kogyo Kabushiki Kaisha | Melted-solidified matter, copper alloy material for melting-solidification, and process for producing the same |
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